Modulated guided surface waves

ABSTRACT

Disclosed are various systems and methods directed to the launching of a guided surface wave embodying a modulated signal using a guided surface waveguide probe. A modulated signal is generated and coupled to a guided surface waveguide probe. A resulting guided surface wave is launched that decays exponentially as a function of distance.

CROSS REFERENCE TO RELATED APPLICATIONS

This application claims the benefit of, and priority to, U.S. Provisional Patent Application No. 62/049,302 entitled “AMPLITUDE MODULATED GUIDED SURFACE WAVES” filed on Sep. 11, 2014, which is incorporated herein by reference in its entirety.

BACKGROUND

For over a century, signals transmitted by radio waves involved radiation fields launched using conventional antenna structures. In contrast to radio science, electrical power distribution systems in the last century involved the transmission of energy guided along electrical conductors. This understanding of the distinction between radio frequency (RF) and power transmission has existed since the early 1900's.

BRIEF DESCRIPTION OF THE DRAWINGS

Many aspects of the present disclosure can be better understood with reference to the following drawings. The components in the drawings are not necessarily to scale, emphasis instead being placed upon clearly illustrating the principles of the disclosure. Moreover, in the drawings, like reference numerals designate corresponding parts throughout the several views.

FIG. 1 is a chart that depicts field strength as a function of distance for a guided electromagnetic field and a radiated electromagnetic field.

FIG. 2 is a drawing that illustrates a propagation interface with two regions employed for transmission of a guided surface wave according to various embodiments of the present disclosure.

FIG. 3 is a drawing that illustrates a guided surface waveguide probe disposed with respect to a propagation interface of FIG. 2 according to various embodiments of the present disclosure.

FIG. 4 is a plot of an example of the magnitudes of close-in and far-out asymptotes of first order Hankel functions according to various embodiments of the present disclosure.

FIGS. 5A and 5B are drawings that illustrate a complex angle of incidence of an electric field synthesized by a guided surface waveguide probe according to various embodiments of the present disclosure.

FIG. 6 is a graphical representation illustrating the effect of elevation of a charge terminal on the location where the electric field of FIG. 5A intersects with the lossy conducting medium at a Brewster angle according to various embodiments of the present disclosure.

FIG. 7 is a graphical representation of an example of a guided surface waveguide probe according to various embodiments of the present disclosure.

FIGS. 8A through 8C are graphical representations illustrating examples of equivalent image plane models of the guided surface waveguide probe of FIGS. 3 and 7 according to various embodiments of the present disclosure.

FIGS. 9A and 9B are graphical representations illustrating examples of single-wire transmission line and classic transmission line models of the equivalent image plane models of FIGS. 8B and 8C according to various embodiments of the present disclosure.

FIG. 10 is a flow chart illustrating an example of adjusting a guided surface waveguide probe of FIGS. 3 and 7 to launch a guided surface wave along the surface of a lossy conducting medium according to various embodiments of the present disclosure.

FIG. 11 is a plot illustrating an example of the relationship between a wave tilt angle and the phase delay of a guided surface waveguide probe of FIGS. 3 and 7 according to various embodiments of the present disclosure.

FIG. 12 is a drawing that illustrates an example of a guided surface waveguide probe according to various embodiments of the present disclosure.

FIG. 13 is a graphical representation illustrating the incidence of a synthesized electric field at a complex Brewster angle to match the guided surface waveguide mode at the Hankel crossover distance according to various embodiments of the present disclosure.

FIG. 14 is a graphical representation of an example of a guided surface waveguide probe of FIG. 12 according to various embodiments of the present disclosure.

FIG. 15A includes plots of an example of the imaginary and real parts of a phase delay (Φ_(U)) of a charge terminal T₁ of a guided surface waveguide probe according to various embodiments of the present disclosure.

FIG. 15B is a schematic diagram of the guided surface waveguide probe of FIG. 14 according to various embodiments of the present disclosure.

FIG. 16 is a drawing that illustrates an example of a guided surface waveguide probe according to various embodiments of the present disclosure.

FIG. 17 is a graphical representation of an example of a guided surface waveguide probe of FIG. 16 according to various embodiments of the present disclosure.

FIGS. 18A through 18C depict examples of receiving structures that can be employed to receive energy transmitted in the form of a guided surface wave launched by a guided surface waveguide probe according to the various embodiments of the present disclosure.

FIG. 18D is a flow chart illustrating an example of adjusting a receiving structure according to various embodiments of the present disclosure.

FIG. 19 depicts an example of an additional receiving structure that can be employed to receive energy transmitted in the form of a guided surface wave launched by a guided surface waveguide probe according to the various embodiments of the present disclosure.

FIGS. 20A-20E depict schematic symbols of guided surface waveguide probes and guided surface wave receiver structures according to various embodiments of the present disclosure.

FIGS. 21-25 depict schematic diagrams of examples of Amplitude Modulation (AM) transmission systems according to various embodiments of the present disclosure.

FIG. 26 is a drawing that depicts skywave and ground wave propagation that occurs in conventional radio transmission.

FIG. 27 is a drawing of adjacent Amplitude Modulation transmission systems according to various embodiments of the present disclosure.

FIG. 28 is a drawing of adjacent areas served by respective Amplitude Modulation transmission systems according to various embodiments of the present disclosure.

DETAILED DESCRIPTION

To begin, some terminology shall be established to provide clarity in the discussion of concepts to follow. First, as contemplated herein, a formal distinction is drawn between radiated electromagnetic fields and guided electromagnetic fields.

As contemplated herein, a radiated electromagnetic field comprises electromagnetic energy that is emitted from a source structure in the form of waves that are not bound to a waveguide. For example, a radiated electromagnetic field is generally a field that leaves an electric structure such as an antenna and propagates through the atmosphere or other medium and is not bound to any waveguide structure. Once radiated electromagnetic waves leave an electric structure such as an antenna, they continue to propagate in the medium of propagation (such as air) independent of their source until they dissipate regardless of whether the source continues to operate. Once electromagnetic waves are radiated, they are not recoverable unless intercepted, and, if not intercepted, the energy inherent in the radiated electromagnetic waves is lost forever. Electrical structures such as antennas are designed to radiate electromagnetic fields by maximizing the ratio of the radiation resistance to the structure loss resistance. Radiated energy spreads out in space and is lost regardless of whether a receiver is present. The energy density of the radiated fields is a function of distance due to geometric spreading. Accordingly, the term “radiate” in all its forms as used herein refers to this form of electromagnetic propagation.

A guided electromagnetic field is a propagating electromagnetic wave whose energy is concentrated within or near boundaries between media having different electromagnetic properties. In this sense, a guided electromagnetic field is one that is bound to a waveguide and may be characterized as being conveyed by the current flowing in the waveguide. If there is no load to receive and/or dissipate the energy conveyed in a guided electromagnetic wave, then no energy is lost except for that dissipated in the conductivity of the guiding medium. Stated another way, if there is no load for a guided electromagnetic wave, then no energy is consumed. Thus, a generator or other source generating a guided electromagnetic field does not deliver real power unless a resistive load is present. To this end, such a generator or other source essentially runs idle until a load is presented. This is akin to running a generator to generate a 60 Hertz electromagnetic wave that is transmitted over power lines where there is no electrical load. It should be noted that a guided electromagnetic field or wave is the equivalent to what is termed a “transmission line mode.” This contrasts with radiated electromagnetic waves in which real power is supplied at all times in order to generate radiated waves. Unlike radiated electromagnetic waves, guided electromagnetic energy does not continue to propagate along a finite length waveguide after the energy source is turned off. Accordingly, the term “guide” in all its forms as used herein refers to this transmission mode of electromagnetic propagation.

Referring now to FIG. 1, shown is a graph 100 of field strength in decibels (dB) above an arbitrary reference in volts per meter as a function of distance in kilometers on a log-dB plot to further illustrate the distinction between radiated and guided electromagnetic fields. The graph 100 of FIG. 1 depicts a guided field strength curve 103 that shows the field strength of a guided electromagnetic field as a function of distance. This guided field strength curve 103 is essentially the same as a transmission line mode. Also, the graph 100 of FIG. 1 depicts a radiated field strength curve 106 that shows the field strength of a radiated electromagnetic field as a function of distance.

Of interest are the shapes of the curves 103 and 106 for guided wave and for radiation propagation, respectively. The radiated field strength curve 106 falls off geometrically (1/d, where d is distance), which is depicted as a straight line on the log-log scale. The guided field strength curve 103, on the other hand, has a characteristic exponential decay of e^(−αd)/√{square root over (d)} and exhibits a distinctive knee 109 on the log-log scale. The guided field strength curve 103 and the radiated field strength curve 106 intersect at point 112, which occurs at a crossing distance. At distances less than the crossing distance at intersection point 112, the field strength of a guided electromagnetic field is significantly greater at most locations than the field strength of a radiated electromagnetic field. At distances greater than the crossing distance, the opposite is true. Thus, the guided and radiated field strength curves 103 and 106 further illustrate the fundamental propagation difference between guided and radiated electromagnetic fields. For an informal discussion of the difference between guided and radiated electromagnetic fields, reference is made to Milligan, T., Modern Antenna Design, McGraw-Hill, 1^(st) Edition, 1985, pp. 8-9, which is incorporated herein by reference in its entirety.

The distinction between radiated and guided electromagnetic waves, made above, is readily expressed formally and placed on a rigorous basis. That two such diverse solutions could emerge from one and the same linear partial differential equation, the wave equation, analytically follows from the boundary conditions imposed on the problem. The Green function for the wave equation, itself, contains the distinction between the nature of radiation and guided waves.

In empty space, the wave equation is a differential operator whose eigenfunctions possess a continuous spectrum of eigenvalues on the complex wave-number plane. This transverse electro-magnetic (TEM) field is called the radiation field, and those propagating fields are called “Hertzian waves.” However, in the presence of a conducting boundary, the wave equation plus boundary conditions mathematically lead to a spectral representation of wave-numbers composed of a continuous spectrum plus a sum of discrete spectra. To this end, reference is made to Sommerfeld, A., “Uber die Ausbreitung der Wellen in der Drahtlosen Telegraphie,” Annalen der Physik, Vol. 28, 1909, pp. 665-736. Also see Sommerfeld, A., “Problems of Radio,” published as Chapter 6 in Partial Differential Equations in Physics—Lectures on Theoretical Physics: Volume VI, Academic Press, 1949, pp. 236-289, 295-296; Collin, R. E., “Hertzian Dipole Radiating Over a Lossy Earth or Sea: Some Early and Late 20^(th) Century Controversies,” IEEE Antennas and Propagation Magazine, Vol. 46, No. 2, April 2004, pp. 64-79; and Reich, H. J., Ordnung, P. F, Krauss, H. L., and Skalnik, J. G., Microwave Theory and Techniques, Van Nostrand, 1953, pp. 291-293, each of these references being incorporated herein by reference in its entirety.

The terms “ground wave” and “surface wave” identify two distinctly different physical propagation phenomena. A surface wave arises analytically from a distinct pole yielding a discrete component in the plane wave spectrum. See, e.g., “The Excitation of Plane Surface Waves” by Cullen, A. L., (Proceedings of the IEE (British), Vol. 101, Part IV, August 1954, pp. 225-235). In this context, a surface wave is considered to be a guided surface wave. The surface wave (in the Zenneck-Sommerfeld guided wave sense) is, physically and mathematically, not the same as the ground wave (in the Weyl-Norton-FCC sense) that is now so familiar from radio broadcasting. These two propagation mechanisms arise from the excitation of different types of eigenvalue spectra (continuum or discrete) on the complex plane. The field strength of the guided surface wave decays exponentially with distance as illustrated by curve 103 of FIG. 1 (much like propagation in a lossy waveguide) and resembles propagation in a radial transmission line, as opposed to the classical Hertzian radiation of the ground wave, which propagates spherically, possesses a continuum of eigenvalues, falls off geometrically as illustrated by curve 106 of FIG. 1, and results from branch-cut integrals. As experimentally demonstrated by C. R. Burrows in “The Surface Wave in Radio Propagation over Plane Earth” (Proceedings of the IRE, Vol. 25, No. 2, February, 1937, pp. 219-229) and “The Surface Wave in Radio Transmission” (Bell Laboratories Record, Vol. 15, June 1937, pp. 321-324), vertical antennas radiate ground waves but do not launch guided surface waves.

To summarize the above, first, the continuous part of the wave-number eigenvalue spectrum, corresponding to branch-cut integrals, produces the radiation field, and second, the discrete spectra, and corresponding residue sum arising from the poles enclosed by the contour of integration, result in non-TEM traveling surface waves that are exponentially damped in the direction transverse to the propagation. Such surface waves are guided transmission line modes. For further explanation, reference is made to Friedman, B., Principles and Techniques of Applied Mathematics, Wiley, 1956, pp. 214, 283-286, 290, 298-300.

In free space, antennas excite the continuum eigenvalues of the wave equation, which is a radiation field, where the outwardly propagating RF energy with E_(z) and H_(ϕ) in-phase is lost forever. On the other hand, waveguide probes excite discrete eigenvalues, which results in transmission line propagation. See Collin, R. E., Field Theory of Guided Waves, McGraw-Hill, 1960, pp. 453, 474-477. While such theoretical analyses have held out the hypothetical possibility of launching open surface guided waves over planar or spherical surfaces of lossy, homogeneous media, for more than a century no known structures in the engineering arts have existed for accomplishing this with any practical efficiency. Unfortunately, since it emerged in the early 1900's, the theoretical analysis set forth above has essentially remained a theory and there have been no known structures for practically accomplishing the launching of open surface guided waves over planar or spherical surfaces of lossy, homogeneous media.

According to the various embodiments of the present disclosure, various guided surface waveguide probes are described that are configured to excite electric fields that couple into a guided surface waveguide mode along the surface of a lossy conducting medium. Such guided electromagnetic fields are substantially mode-matched in magnitude and phase to a guided surface wave mode on the surface of the lossy conducting medium. Such a guided surface wave mode can also be termed a Zenneck waveguide mode. By virtue of the fact that the resultant fields excited by the guided surface waveguide probes described herein are substantially mode-matched to a guided surface waveguide mode on the surface of the lossy conducting medium, a guided electromagnetic field in the form of a guided surface wave is launched along the surface of the lossy conducting medium. According to one embodiment, the lossy conducting medium comprises a terrestrial medium such as the Earth.

Referring to FIG. 2, shown is a propagation interface that provides for an examination of the boundary value solutions to Maxwell's equations derived in 1907 by Jonathan Zenneck as set forth in his paper Zenneck, J., “On the Propagation of Plane Electromagnetic Waves Along a Flat Conducting Surface and their Relation to Wireless Telegraphy,” Annalen der Physik, Serial 4, Vol. 23, Sep. 20, 1907, pp. 846-866. FIG. 2 depicts cylindrical coordinates for radially propagating waves along the interface between a lossy conducting medium specified as Region 1 and an insulator specified as Region 2. Region 1 can comprise, for example, any lossy conducting medium. In one example, such a lossy conducting medium can comprise a terrestrial medium such as the Earth or other medium. Region 2 is a second medium that shares a boundary interface with Region 1 and has different constitutive parameters relative to Region 1. Region 2 can comprise, for example, any insulator such as the atmosphere or other medium. The reflection coefficient for such a boundary interface goes to zero only for incidence at a complex Brewster angle. See Stratton, J. A., Electromagnetic Theory, McGraw-Hill, 1941, p. 516.

According to various embodiments, the present disclosure sets forth various guided surface waveguide probes that generate electromagnetic fields that are substantially mode-matched to a guided surface waveguide mode on the surface of the lossy conducting medium comprising Region 1. According to various embodiments, such electromagnetic fields substantially synthesize a wave front incident at a complex Brewster angle of the lossy conducting medium that can result in zero reflection.

To explain further, in Region 2, where an e^(jωt) field variation is assumed and where ρ≠0 and z≥0 (with z being the vertical coordinate normal to the surface of Region 1, and ρ being the radial dimension in cylindrical coordinates), Zenneck's closed-form exact solution of Maxwell's equations satisfying the boundary conditions along the interface are expressed by the following electric field and magnetic field components:

$\begin{matrix} {{H_{2\phi} = {A\; e^{{- u_{2}}z}{H_{1}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}}},} & (1) \\ {{E_{2\rho} = {{A\left( \frac{u_{2}}{{j\omega ɛ}_{o}} \right)}e^{{- u_{2}}z}{H_{1}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}}},{and}} & (2) \\ {E_{2\; z} = {{A\left( \frac{- \gamma}{{\omega ɛ}_{o}} \right)}e^{{- u_{2}}z}{{H_{0}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}.}}} & (3) \end{matrix}$

In Region 1, where the e^(jωt) field variation is assumed and where ρ≠0 and z≤0, Zenneck's closed-form exact solution of Maxwell's equations satisfying the boundary conditions along the interface is expressed by the following electric field and magnetic field components:

$\begin{matrix} {{H_{1\phi} = {A\; e^{u_{1}z}{H_{1}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}}},} & (4) \\ {{E_{1\rho} = {{A\left( \frac{- u_{1}}{\sigma_{1} + {j\;{\omega ɛ}_{1}}} \right)}e^{u_{1}z}{H_{1}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}}},{and}} & (5) \\ {E_{1z} = {{A\left( \frac{{- j}\;\gamma}{\sigma_{1} + {j\;{\omega ɛ}_{1}}} \right)}e^{u_{1}z}{{H_{0}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}.}}} & (6) \end{matrix}$

In these expressions, z is the vertical coordinate normal to the surface of Region 1 and ρ is the radial coordinate, H_(n) ⁽²⁾(−jγρ) is a complex argument Hankel function of the second kind and order n, u₁ is the propagation constant in the positive vertical (z) direction in Region 1, u₂ is the propagation constant in the vertical (z) direction in Region 2, σ₁ is the conductivity of Region 1, ω is equal to 2πf, where f is a frequency of excitation, ε_(o) is the permittivity of free space, ε₁ is the permittivity of Region 1, A is a source constant imposed by the source, and γ is a surface wave radial propagation constant.

The propagation constants in the ±z directions are determined by separating the wave equation above and below the interface between Regions 1 and 2, and imposing the boundary conditions. This exercise gives, in Region 2,

$\begin{matrix} {u_{2} = \frac{{- j}\mspace{11mu} k_{o}}{\sqrt{1 + \left( {ɛ_{r} - {j\mspace{11mu} x}} \right)}}} & (7) \end{matrix}$ and gives, in Region 1, u ₁ =−u ₂(ε_(r) −jx).  (8) The radial propagation constant γ is given by

$\begin{matrix} {{\gamma = {{j\sqrt{k_{o}^{2} + u_{2}^{2}}} = {j\frac{k_{o}n}{\sqrt{1 + n^{2}}}}}},} & (9) \end{matrix}$ which is a complex expression where n is the complex index of refraction given by n=√{square root over (ε_(r) −jx)}.  (10) In all of the above Equations,

$\begin{matrix} {{x = \frac{\sigma_{1}}{{\omega ɛ}_{o}}},{and}} & (11) \\ {{k_{o} = {{\omega\sqrt{\mu_{o}ɛ_{o}}} = \frac{\lambda_{o}}{2\pi}}},} & (12) \end{matrix}$ where ε_(r) comprises the relative permittivity of Region 1, σ₁ is the conductivity of Region 1, ε_(o) is the permittivity of free space, and μ_(o) comprises the permeability of free space. Thus, the generated surface wave propagates parallel to the interface and exponentially decays vertical to it. This is known as evanescence.

Thus, Equations (1)-(3) can be considered to be a cylindrically-symmetric, radially-propagating waveguide mode. See Barlow, H. M., and Brown, J., Radio Surface Waves, Oxford University Press, 1962, pp. 10-12, 29-33. The present disclosure details structures that excite this “open boundary” waveguide mode. Specifically, according to various embodiments, a guided surface waveguide probe is provided with a charge terminal of appropriate size that is fed with voltage and/or current and is positioned relative to the boundary interface between Region 2 and Region 1. This may be better understood with reference to FIG. 3, which shows an example of a guided surface waveguide probe 200 a that includes a charge terminal T₁ elevated above a lossy conducting medium 203 (e.g., the Earth) along a vertical axis z that is normal to a plane presented by the lossy conducting medium 203. The lossy conducting medium 203 makes up Region 1, and a second medium 206 makes up Region 2 and shares a boundary interface with the lossy conducting medium 203.

According to one embodiment, the lossy conducting medium 203 can comprise a terrestrial medium such as the planet Earth. To this end, such a terrestrial medium comprises all structures or formations included thereon whether natural or man-made. For example, such a terrestrial medium can comprise natural elements such as rock, soil, sand, fresh water, sea water, trees, vegetation, and all other natural elements that make up our planet. In addition, such a terrestrial medium can comprise man-made elements such as concrete, asphalt, building materials, and other man-made materials. In other embodiments, the lossy conducting medium 203 can comprise some medium other than the Earth, whether naturally occurring or man-made. In other embodiments, the lossy conducting medium 203 can comprise other media such as man-made surfaces and structures such as automobiles, aircraft, man-made materials (such as plywood, plastic sheeting, or other materials) or other media.

In the case where the lossy conducting medium 203 comprises a terrestrial medium or Earth, the second medium 206 can comprise the atmosphere above the ground. As such, the atmosphere can be termed an “atmospheric medium” that comprises air and other elements that make up the atmosphere of the Earth. In addition, it is possible that the second medium 206 can comprise other media relative to the lossy conducting medium 203.

The guided surface waveguide probe 200 a includes a feed network 209 that couples an excitation source 212 to the charge terminal T₁ via, e.g., a vertical feed line conductor and/or other components as will be described. According to various embodiments, a charge Q₁ is imposed on the charge terminal T₁ to synthesize an electric field based upon the voltage applied to terminal T₁ at any given instant. Depending on the angle of incidence (θ_(i)) of the electric field (E), it is possible to substantially mode-match the electric field to a guided surface waveguide mode on the surface of the lossy conducting medium 203 comprising Region 1.

By considering the Zenneck closed-form solutions of Equations (1)-(6), the Leontovich impedance boundary condition between Region 1 and Region 2 can be stated as {circumflex over (z)}×

(ρ,φ,0)={right arrow over (J)} _(S),  (13) where {circumflex over (z)} is a unit normal in the positive vertical (+z) direction and {right arrow over (H)}₂ is the magnetic field strength in Region 2 expressed by Equation (1) above. Equation (13) implies that the electric and magnetic fields specified in Equations (1)-(3) may result in a radial surface current density along the boundary interface, where the radial surface current density can be specified by J _(ρ)(ρ′)=−AH ₁ ⁽²⁾(−jγρ′)  (14) where A is a constant. Further, it should be noted that close-in to the guided surface waveguide probe 200 (for ρ<<λ), Equation (14) above has the behavior

$\begin{matrix} {{J_{close}\left( \rho^{\prime} \right)} = {\frac{- {A\left( {j\mspace{11mu} 2} \right)}}{\pi\left( {{- j}\;{\gamma\rho}^{\prime}} \right)} = {{- H_{\phi}} = {- {\frac{I_{o}}{2{\pi\rho}^{\prime}}.}}}}} & (15) \end{matrix}$ The negative sign means that when source current (I_(o)) flows vertically upward as illustrated in FIG. 3, the “close-in” ground current flows radially inward. By field matching on H_(ϕ) “close-in,” it can be determined that

$\begin{matrix} {A = {\frac{I_{o}\gamma}{4} = {- \frac{\omega\; q_{1}\gamma}{4}}}} & (16) \end{matrix}$ where q₁=C₁V₁, in Equations (1)-(6) and (14). Therefore, the radial surface current density of Equation (14) can be restated as

$\begin{matrix} {{J_{\rho}\left( \rho^{\prime} \right)} = {\frac{I_{o}\gamma}{4}{{H_{1}^{(2)}\left( {{- j}\;{\gamma\rho}^{\prime}} \right)}.}}} & (17) \end{matrix}$ The fields expressed by Equations (1)-(6) and (17) have the nature of a transmission line mode bound to a lossy interface, not radiation fields that are associated with groundwave propagation. See Barlow, H. M. and Brown, J., Radio Surface Waves, Oxford University Press, 1962, pp. 1-5.

At this point, a review of the nature of the Hankel functions used in Equations (1)-(6) and (17) is provided for these solutions of the wave equation. One might observe that the Hankel functions of the first and second kind and order n are defined as complex combinations of the standard Bessel functions of the first and second kinds H _(n) ⁽¹⁾(x)=J _(n)(x)+jN _(n)(x), and  (18) H _(n) ⁽²⁾(x)=J _(n)(x)−jN _(n)(x),  (19) These functions represent cylindrical waves propagating radially inward (H_(n) ⁽¹⁾) and outward (H_(n) ⁽²⁾), respectively. The definition is analogous to the relationship e^(±jx)=cos x±j sin x. See, for example, Harrington, R. F., Time-Harmonic Fields, McGraw-Hill, 1961, pp. 460-463.

That H_(n) ⁽²⁾(k_(ρ)ρ) is an outgoing wave can be recognized from its large argument asymptotic behavior that is obtained directly from the series definitions of J_(n)(x) and N_(n)(x). Far-out from the guided surface waveguide probe:

$\begin{matrix} {{{{{H_{n}^{(2)}(x)}\underset{\;{x->\infty}\mspace{14mu}}{\longrightarrow}\sqrt{\frac{2j}{\pi\; x}}}j^{n}e^{{- j}\; x}} = {\sqrt{\frac{2}{\pi\; x}}j^{n}e^{{- j}\;{({x - \frac{\pi}{4}})}}}},} & \left( {20a} \right) \end{matrix}$ which, when multiplied by e^(jωt), is an outward propagating cylindrical wave of the form e^(j(ωt-kρ)) with a 1/√{square root over (ρ)} spatial variation. The first order (n=1) solution can be determined from Equation (20a) to be

$\begin{matrix} {{{{H_{1}^{(2)}(x)}\underset{{x->\infty}\mspace{14mu}}{\longrightarrow}j}\sqrt{\frac{2j}{\pi\; x}}e^{{- j}\; x}} = {\sqrt{\frac{2}{\pi\; x}}{e^{{- j}\;{({x - \frac{\pi}{2} - \frac{\pi}{4}})}}.}}} & \left( {20b} \right) \end{matrix}$ Close-in to the guided surface waveguide probe (for ρ<<λ), the Hankel function of first order and the second kind behaves as

$\begin{matrix} {{{H_{1}^{(2)}(x)}\underset{\;{x->0}\mspace{11mu}}{\longrightarrow}\frac{2j}{\pi\; x}}.} & (21) \end{matrix}$ Note that these asymptotic expressions are complex quantities. When x is a real quantity, Equations (20b) and (21) differ in phase by √{square root over (j)}, which corresponds to an extra phase advance or “phase boost” of 45° or, equivalently, λ/8. The close-in and far-out asymptotes of the first order Hankel function of the second kind have a Hankel “crossover” or transition point where they are of equal magnitude at a distance of ρ=R_(x).

Thus, beyond the Hankel crossover point the “far out” representation predominates over the “close-in” representation of the Hankel function. The distance to the Hankel crossover point (or Hankel crossover distance) can be found by equating Equations (20b) and (21) for −jγρ, and solving for R_(x). With x=σ/ωε_(o), it can be seen that the far-out and close-in Hankel function asymptotes are frequency dependent, with the Hankel crossover point moving out as the frequency is lowered. It should also be noted that the Hankel function asymptotes may also vary as the conductivity (σ) of the lossy conducting medium changes. For example, the conductivity of the soil can vary with changes in weather conditions.

Referring to FIG. 4, shown is an example of a plot of the magnitudes of the first order Hankel functions of Equations (20b) and (21) for a Region 1 conductivity of σ=0.010 mhos/m and relative permittivity ε_(r)=15, at an operating frequency of 1850 kHz. Curve 115 is the magnitude of the far-out asymptote of Equation (20b) and curve 118 is the magnitude of the close-in asymptote of Equation (21), with the Hankel crossover point 121 occurring at a distance of R_(x)=54 feet. While the magnitudes are equal, a phase offset exists between the two asymptotes at the Hankel crossover point 121. It can also be seen that the Hankel crossover distance is much less than a wavelength of the operation frequency.

Considering the electric field components given by Equations (2) and (3) of the Zenneck closed-form solution in Region 2, it can be seen that the ratio of E_(z) and E_(ρ) asymptotically passes to

$\begin{matrix} {{\frac{E_{z}}{E_{\rho}} = {{\left( \frac{{- j}\;\gamma}{u_{2}} \right){\frac{H_{0}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}{H_{1}^{(2)}\left( {{- j}\;{\gamma\rho}} \right)}\underset{\rho->\infty}{\longrightarrow}\sqrt{ɛ_{r} - {j\;\frac{\sigma}{{\omega ɛ}_{o}}}}}} = {n = {\tan\mspace{11mu}\theta_{i}}}}},} & (22) \end{matrix}$ where n is the complex index of refraction of Equation (10) and θ_(i) is the angle of incidence of the electric field. In addition, the vertical component of the mode-matched electric field of Equation (3) asymptotically passes to

$\begin{matrix} {{{E_{2z}\underset{{\rho->\infty}\mspace{11mu}}{\longrightarrow}\left( \frac{q_{free}}{ɛ_{o}} \right)}\sqrt{\frac{\gamma^{3}}{8\pi}}e^{{- u_{2}}z}\frac{e^{- {j{({{\gamma\rho} - {\pi/4}})}}}}{\sqrt{\rho}}},} & (23) \end{matrix}$ which is linearly proportional to free charge on the isolated component of the elevated charge terminal's capacitance at the terminal voltage, q_(free)=C_(free)×V_(T).

For example, the height H₁ of the elevated charge terminal T₁ in FIG. 3 affects the amount of free charge on the charge terminal T₁. When the charge terminal T₁ is near the ground plane of Region 1, most of the charge Q₁ on the terminal is “bound.” As the charge terminal T₁ is elevated, the bound charge is lessened until the charge terminal T₁ reaches a height at which substantially all of the isolated charge is free.

The advantage of an increased capacitive elevation for the charge terminal T₁ is that the charge on the elevated charge terminal T₁ is further removed from the ground plane, resulting in an increased amount of free charge q_(free) to couple energy into the guided surface waveguide mode. As the charge terminal T₁ is moved away from the ground plane, the charge distribution becomes more uniformly distributed about the surface of the terminal. The amount of free charge is related to the self-capacitance of the charge terminal T₁.

For example, the capacitance of a spherical terminal can be expressed as a function of physical height above the ground plane. The capacitance of a sphere at a physical height of h above a perfect ground is given by C _(elevated sphere)=4πε_(o) a(1+M+M ² +M ³+2M ⁴+3M ⁵+ . . . ),  (24) where the diameter of the sphere is 2a, and where M=a/2h with h being the height of the spherical terminal. As can be seen, an increase in the terminal height h reduces the capacitance C of the charge terminal. It can be shown that for elevations of the charge terminal T₁ that are at a height of about four times the diameter (4D=8a) or greater, the charge distribution is approximately uniform about the spherical terminal, which can improve the coupling into the guided surface waveguide mode.

In the case of a sufficiently isolated terminal, the self-capacitance of a conductive sphere can be approximated by C=4πε_(o)a, where a is the radius of the sphere in meters, and the self-capacitance of a disk can be approximated by C=8ε_(o)a, where a is the radius of the disk in meters. The charge terminal T₁ can include any shape such as a sphere, a disk, a cylinder, a cone, a torus, a hood, one or more rings, or any other randomized shape or combination of shapes. An equivalent spherical diameter can be determined and used for positioning of the charge terminal T₁.

This may be further understood with reference to the example of FIG. 3, where the charge terminal T₁ is elevated at a physical height of h_(p)=H₁ above the lossy conducting medium 203. To reduce the effects of the “bound” charge, the charge terminal T₁ can be positioned at a physical height that is at least four times the spherical diameter (or equivalent spherical diameter) of the charge terminal T₁ to reduce the bounded charge effects.

Referring next to FIG. 5A, shown is a ray optics interpretation of the electric field produced by the elevated charge Q₁ on charge terminal T₁ of FIG. 3. As in optics, minimizing the reflection of the incident electric field can improve and/or maximize the energy coupled into the guided surface waveguide mode of the lossy conducting medium 203. For an electric field (E_(∥)) that is polarized parallel to the plane of incidence (not the boundary interface), the amount of reflection of the incident electric field may be determined using the Fresnel reflection coefficient, which can be expressed as

$\begin{matrix} {{{\Gamma_{❘❘}\left( \theta_{i} \right)} = {\frac{E_{{❘❘},R}}{E_{{❘❘},i}} = \frac{\sqrt{\left( {ɛ_{r} - {j\; x}} \right) - {\sin^{2}\mspace{11mu}\theta_{i}}} - {\left( {ɛ_{r} - {j\; x}} \right)\mspace{11mu}\cos\mspace{11mu}\theta_{i}}}{\sqrt{\left( {ɛ_{r} - {j\; x}} \right) - {\sin^{2}\mspace{11mu}\theta_{i}}} + {\left( {ɛ_{r} - {j\; x}} \right)\mspace{11mu}\cos\mspace{11mu}\theta_{i}}}}},} & (25) \end{matrix}$ where θ_(i) is the conventional angle of incidence measured with respect to the surface normal.

In the example of FIG. 5A, the ray optic interpretation shows the incident field polarized parallel to the plane of incidence having an angle of incidence of θ_(i), which is measured with respect to the surface normal ({circumflex over (z)}). There will be no reflection of the incident electric field when Γ_(∥)(θ_(i))=0 and thus the incident electric field will be completely coupled into a guided surface waveguide mode along the surface of the lossy conducting medium 203. It can be seen that the numerator of Equation (25) goes to zero when the angle of incidence is θ_(i)=arctan(√{square root over (ε_(r) −jx)})=θ_(i,B),  (26) where x=σ/ωε_(o). This complex angle of incidence (θ_(i,B)) is referred to as the Brewster angle. Referring back to Equation (22), it can be seen that the same complex Brewster angle (θ_(i,B)) relationship is present in both Equations (22) and (26).

As illustrated in FIG. 5A, the electric field vector E can be depicted as an incoming non-uniform plane wave, polarized parallel to the plane of incidence. The electric field vector E can be created from independent horizontal and vertical components as {right arrow over (E)}(θ_(i))=E _(ρ) ρ+E _(z) {circumflex over (z)}.  (27) Geometrically, the illustration in FIG. 5A suggests that the electric field vector E can be given by

$\begin{matrix} {{{E_{\rho}\left( {\rho,z} \right)} = {{E\left( {\rho,z} \right)}\mspace{11mu}\cos\mspace{11mu}\theta_{i}}},{and}} & \left( {28a} \right) \\ {{{E_{z}\left( {\rho,z} \right)} = {{{E\left( {\rho,z} \right)}\mspace{11mu}{\cos\left( {\frac{\pi}{2} - \theta_{i}} \right)}} = {{E\left( {\rho,z} \right)}\mspace{11mu}\sin\mspace{11mu}\theta_{i}}}},} & \left( {28b} \right) \end{matrix}$ which means that the field ratio is

$\begin{matrix} {\frac{E_{\rho}}{E_{z}} = {\frac{1}{\tan\mspace{11mu}\theta_{i}} = {\tan\mspace{14mu}{\psi_{i}.}}}} & (29) \end{matrix}$

A generalized parameter W, called “wave tilt,” is noted herein as the ratio of the horizontal electric field component to the vertical electric field component given by

$\begin{matrix} {{W = {\frac{E_{\rho}}{E_{z}} = {{W}e^{j\;\Psi}}}},{or}} & \left( {30a} \right) \\ {{\frac{1}{W} = {\frac{E_{z}}{E_{\rho}} = {{\tan\mspace{11mu}\theta_{i}} = {\frac{1}{W}e^{{- j}\;\Psi}}}}},} & \left( {30b} \right) \end{matrix}$ which is complex and has both magnitude and phase. For an electromagnetic wave in Region 2, the wave tilt angle (Ψ) is equal to the angle between the normal of the wave-front at the boundary interface with Region 1 and the tangent to the boundary interface. This may be easier to see in FIG. 5B, which illustrates equi-phase surfaces of an electromagnetic wave and their normals for a radial cylindrical guided surface wave. At the boundary interface (z=0) with a perfect conductor, the wave-front normal is parallel to the tangent of the boundary interface, resulting in W=0. However, in the case of a lossy dielectric, a wave tilt W exists because the wave-front normal is not parallel with the tangent of the boundary interface at z=0.

Applying Equation (30b) to a guided surface wave gives

$\begin{matrix} {{\tan\mspace{11mu}\theta_{i,B}} = {\frac{E_{z}}{E_{\rho}} = {\frac{u_{2}}{\gamma} = {\sqrt{ɛ_{r} - {j\; x}} = {n = {\frac{1}{W} = {\frac{1}{W}{e^{{- j}\;\Psi}.}}}}}}}} & (31) \end{matrix}$ With the angle of incidence equal to the complex Brewster angle (θ_(i,B)), the Fresnel reflection coefficient of Equation (25) vanishes, as shown by

$\begin{matrix} {{\Gamma_{❘❘}\left( \theta_{i,B} \right)} = {{\frac{\sqrt{\left( {ɛ_{r} - {j\; x}} \right) - {\sin^{2}\mspace{11mu}\theta_{i}}} - {\left( {ɛ_{r} - {j\; x}} \right)\mspace{11mu}\cos\mspace{11mu}\theta_{i}}}{\sqrt{\left( {ɛ_{r} - {j\; x}} \right) - {\sin^{2}\mspace{11mu}\theta_{i}}} + {\left( {ɛ_{r} - {j\; x}} \right)\mspace{11mu}\cos\mspace{11mu}\theta_{i}}}❘_{\theta_{i} = \theta_{i,B}}} = 0.}} & (32) \end{matrix}$ By adjusting the complex field ratio of Equation (22), an incident field can be synthesized to be incident at a complex angle at which the reflection is reduced or eliminated. Establishing this ratio as n=√{square root over (ε_(r)−jx)} results in the synthesized electric field being incident at the complex Brewster angle, making the reflections vanish.

The concept of an electrical effective height can provide further insight into synthesizing an electric field with a complex angle of incidence with a guided surface waveguide probe 200. The electrical effective height (h_(eff)) has been defined as

$\begin{matrix} {h_{eff} = {\frac{1}{I_{0}}{\int_{0}^{h_{p}}{{I(z)}\ d\; z}}}} & (33) \end{matrix}$ for a monopole with a physical height (or length) of h_(p). Since the expression depends upon the magnitude and phase of the source distribution along the structure, the effective height (or length) is complex in general. The integration of the distributed current I(z) of the structure is performed over the physical height of the structure (h_(p)), and normalized to the ground current (I₀) flowing upward through the base (or input) of the structure. The distributed current along the structure can be expressed by I(z)=I _(C) cos(β₀ z),  (34) where β₀ is the propagation factor for current propagating on the structure. In the example of FIG. 3, I_(C) is the current that is distributed along the vertical structure of the guided surface waveguide probe 200 a.

For example, consider a feed network 209 that includes a low loss coil (e.g., a helical coil) at the bottom of the structure and a vertical feed line conductor connected between the coil and the charge terminal T₁. The phase delay due to the coil (or helical delay line) is θ_(c)=β_(p)l_(C), with a physical length of l_(C) and a propagation factor of

$\begin{matrix} {{\beta_{p} = {\frac{2\pi}{\lambda_{p}} = \frac{2\pi}{V_{f}\lambda_{0}}}},} & (35) \end{matrix}$ where V_(f) is the velocity factor on the structure, λ₀ is the wavelength at the supplied frequency, and λ_(p) is the propagation wavelength resulting from the velocity factor V_(f). The phase delay is measured relative to the ground (stake) current I₀.

In addition, the spatial phase delay along the length l_(w) of the vertical feed line conductor can be given by θ_(y)=β_(w)l_(w) where β_(w) is the propagation phase constant for the vertical feed line conductor. In some implementations, the spatial phase delay may be approximated by θ_(y)=β_(w)h_(p), since the difference between the physical height h_(p) of the guided surface waveguide probe 200 a and the vertical feed line conductor length l_(w) is much less than a wavelength at the supplied frequency (λ₀). As a result, the total phase delay through the coil and vertical feed line conductor is Φ=θ_(c)+θ_(y), and the current fed to the top of the coil from the bottom of the physical structure is I _(C)(θ_(c)+θ_(y))=I ₀ e ^(jΦ),  (36) with the total phase delay Φ measured relative to the ground (stake) current I₀. Consequently, the electrical effective height of a guided surface waveguide probe 200 can be approximated by

$\begin{matrix} {{h_{eff} = {{\frac{1}{I_{0}}{\int_{0}^{h_{p}}{I_{0}e^{j\;\Phi}{\cos\left( {\beta_{0}z} \right)}d\; z}}} \cong {h_{p}e^{j\;\Phi}}}},} & (37) \end{matrix}$ for the case where the physical height h_(p)<<λ₀. The complex effective height of a monopole, h_(eff)=h_(p) at an angle (or phase shift) of Φ, may be adjusted to cause the source fields to match a guided surface waveguide mode and cause a guided surface wave to be launched on the lossy conducting medium 203.

In the example of FIG. 5A, ray optics are used to illustrate the complex angle trigonometry of the incident electric field (E) having a complex Brewster angle of incidence (θ_(i,B)) at the Hankel crossover distance (R_(x)) 121. Recall from Equation (26) that, for a lossy conducting medium, the Brewster angle is complex and specified by

$\begin{matrix} {{\tan\;\theta_{i,B}} = {\sqrt{ɛ_{r} - {j\frac{\sigma}{\omega\; ɛ_{o}}}} = {n.}}} & (38) \end{matrix}$ Electrically, the geometric parameters are related by the electrical effective height (h_(eff)) of the charge terminal T₁ by R _(x) tan ψ_(i,B) =R _(x) ×W=h _(eff) =h _(p) e ^(jΦ),  (39) where ψ_(i,B)=(π/2)−θ_(i,B) is the Brewster angle measured from the surface of the lossy conducting medium. To couple into the guided surface waveguide mode, the wave tilt of the electric field at the Hankel crossover distance can be expressed as the ratio of the electrical effective height and the Hankel crossover distance

$\begin{matrix} {\frac{h_{eff}}{R_{x}} = {{\tan\;\psi_{i,B}} = {W_{R\; x}.}}} & (40) \end{matrix}$ Since both the physical height (h_(p)) and the Hankel crossover distance (R_(x)) are real quantities, the angle (Ψ) of the desired guided surface wave tilt at the Hankel crossover distance (R_(x)) is equal to the phase (Φ) of the complex effective height (h_(eff)). This implies that by varying the phase at the supply point of the coil, and thus the phase shift in Equation (37), the phase, Φ, of the complex effective height can be manipulated to match the angle of the wave tilt, Ψ, of the guided surface waveguide mode at the Hankel crossover point 121: Φ=Ψ.

In FIG. 5A, a right triangle is depicted having an adjacent side of length R_(x) along the lossy conducting medium surface and a complex Brewster angle ψ_(i,B) measured between a ray 124 extending between the Hankel crossover point 121 at R_(x) and the center of the charge terminal T₁, and the lossy conducting medium surface 127 between the Hankel crossover point 121 and the charge terminal T₁. With the charge terminal T₁ positioned at physical height h_(p) and excited with a charge having the appropriate phase delay Φ, the resulting electric field is incident with the lossy conducting medium boundary interface at the Hankel crossover distance R_(x), and at the Brewster angle. Under these conditions, the guided surface waveguide mode can be excited without reflection or substantially negligible reflection.

If the physical height of the charge terminal T₁ is decreased without changing the phase shift Φ of the effective height (h_(eff)), the resulting electric field intersects the lossy conducting medium 203 at the Brewster angle at a reduced distance from the guided surface waveguide probe 200. FIG. 6 graphically illustrates the effect of decreasing the physical height of the charge terminal T₁ on the distance where the electric field is incident at the Brewster angle. As the height is decreased from h₃ through h₂ to h₁, the point where the electric field intersects with the lossy conducting medium (e.g., the Earth) at the Brewster angle moves closer to the charge terminal position. However, as Equation (39) indicates, the height H₁ (FIG. 3) of the charge terminal T₁ should be at or higher than the physical height (h_(p)) in order to excite the far-out component of the Hankel function. With the charge terminal T₁ positioned at or above the effective height (h_(eff)), the lossy conducting medium 203 can be illuminated at the Brewster angle of incidence (ψ_(i,B)=(π/2)−θ_(i,B)) at or beyond the Hankel crossover distance (R_(x)) 121 as illustrated in FIG. 5A. To reduce or minimize the bound charge on the charge terminal T₁, the height should be at least four times the spherical diameter (or equivalent spherical diameter) of the charge terminal T₁ as mentioned above.

A guided surface waveguide probe 200 can be configured to establish an electric field having a wave tilt that corresponds to a wave illuminating the surface of the lossy conducting medium 203 at a complex Brewster angle, thereby exciting radial surface currents by substantially mode-matching to a guided surface wave mode at (or beyond) the Hankel crossover point 121 at R_(x).

Referring to FIG. 7, shown is a graphical representation of an example of a guided surface waveguide probe 200 b that includes a charge terminal T₁. An AC source 212 acts as the excitation source for the charge terminal T₁, which is coupled to the guided surface waveguide probe 200 b through a feed network 209 (FIG. 3) comprising a coil 215 such as, e.g., a helical coil. In other implementations, the AC source 212 can be inductively coupled to the coil 215 through a primary coil. In some embodiments, an impedance matching network may be included to improve and/or maximize coupling of the AC source 212 to the coil 215.

As shown in FIG. 7, the guided surface waveguide probe 200 b can include the upper charge terminal T₁ (e.g., a sphere at height h_(p)) that is positioned along a vertical axis z that is substantially normal to the plane presented by the lossy conducting medium 203. A second medium 206 is located above the lossy conducting medium 203. The charge terminal T₁ has a self-capacitance C_(T). During operation, charge Q₁ is imposed on the terminal T₁ depending on the voltage applied to the terminal T₁ at any given instant.

In the example of FIG. 7, the coil 215 is coupled to a ground stake 218 at a first end and to the charge terminal T₁ via a vertical feed line conductor 221. In some implementations, the coil connection to the charge terminal T₁ can be adjusted using a tap 224 of the coil 215 as shown in FIG. 7. The coil 215 can be energized at an operating frequency by the AC source 212 through a tap 227 at a lower portion of the coil 215. In other implementations, the AC source 212 can be inductively coupled to the coil 215 through a primary coil.

The construction and adjustment of the guided surface waveguide probe 200 is based upon various operating conditions, such as the transmission frequency, conditions of the lossy conducting medium (e.g., soil conductivity σ and relative permittivity ε_(r)), and size of the charge terminal T₁. The index of refraction can be calculated from Equations (10) and (11) as n=√{square root over (ε_(r) −jx)},  (41) where x=σ/ωε_(o) with ω=2πf. The conductivity σ and relative permittivity ε_(r) can be determined through test measurements of the lossy conducting medium 203. The complex Brewster angle (θ_(i,B)) measured from the surface normal can also be determined from Equation (26) as θ_(i,B)=arctan(√{square root over (ε_(r) −jx)}),  (42) or measured from the surface as shown in FIG. 5A as

$\begin{matrix} {\psi_{i,B} = {\frac{\pi}{2} - {\theta_{i,B}.}}} & (43) \end{matrix}$ The wave tilt at the Hankel crossover distance (W_(Rx)) can also be found using Equation (40).

The Hankel crossover distance can also be found by equating the magnitudes of Equations (20b) and (21) for −jγρ, and solving for R_(x) as illustrated by FIG. 4. The electrical effective height can then be determined from Equation (39) using the Hankel crossover distance and the complex Brewster angle as h _(eff) =h _(p) e ^(jΦ) =R _(x) tan ψ_(i,B).  (44) As can be seen from Equation (44), the complex effective height (h_(eff)) includes a magnitude that is associated with the physical height (h_(p)) of the charge terminal T₁ and a phase delay (Φ) that is to be associated with the angle (Ψ) of the wave tilt at the Hankel crossover distance (R_(x)). With these variables and the selected charge terminal T₁ configuration, it is possible to determine the configuration of a guided surface waveguide probe 200.

With the charge terminal T₁ positioned at or above the physical height (h_(p)), the feed network 209 (FIG. 3) and/or the vertical feed line connecting the feed network to the charge terminal T₁ can be adjusted to match the phase (Φ) of the charge Q₁ on the charge terminal T₁ to the angle (Ψ) of the wave tilt (W). The size of the charge terminal T₁ can be chosen to provide a sufficiently large surface for the charge Q₁ imposed on the terminals. In general, it is desirable to make the charge terminal T₁ as large as practical. The size of the charge terminal T₁ should be large enough to avoid ionization of the surrounding air, which can result in electrical discharge or sparking around the charge terminal.

The phase delay θ_(c) of a helically-wound coil can be determined from Maxwell's equations as has been discussed by Corum, K. L. and J. F. Corum, “RF Coils, Helical Resonators and Voltage Magnification by Coherent Spatial Modes,” Microwave Review, Vol. 7, No. 2, September 2001, pp. 36-45, which is incorporated herein by reference in its entirety. For a helical coil with H/D>1, the ratio of the velocity of propagation (υ) of a wave along the coil's longitudinal axis to the speed of light (c), or the “velocity factor,” is given by

$\begin{matrix} {{V_{f} = {\frac{\upsilon}{c} = \frac{1}{\sqrt{1 + {20\left( \frac{D}{s} \right)^{2.5}\left( \frac{D}{\lambda_{o}} \right)^{0.5}}}}}},} & (45) \end{matrix}$ where H is the axial length of the solenoidal helix, D is the coil diameter, N is the number of turns of the coil, s=H/N is the turn-to-turn spacing (or helix pitch) of the coil, and λ_(o) is the free-space wavelength. Based upon this relationship, the electrical length, or phase delay, of the helical coil is given by

$\begin{matrix} {\theta_{c} = {{\beta_{p}H} = {{\frac{2\;\pi}{\lambda_{p}}H} = {\frac{2\;\pi}{V_{f}\lambda_{0}}{H.}}}}} & (46) \end{matrix}$ The principle is the same if the helix is wound spirally or is short and fat, but V_(f) and θ_(c) are easier to obtain by experimental measurement. The expression for the characteristic (wave) impedance of a helical transmission line has also been derived as

$\begin{matrix} {Z_{c} = {{\frac{60}{V_{f}}\left\lbrack {{\ln\left( \frac{V_{f}\lambda_{0}}{D} \right)} - 1.027} \right\rbrack}.}} & (47) \end{matrix}$

The spatial phase delay θ_(y) of the structure can be determined using the traveling wave phase delay of the vertical feed line conductor 221 (FIG. 7). The capacitance of a cylindrical vertical conductor above a perfect ground plane can be expressed as

$\begin{matrix} {{{C_{A} = {\frac{2\;\pi\; ɛ_{o}h_{w}}{{\ln\left( \frac{h}{a} \right)} - 1}\mspace{14mu}{Farads}}},}\;} & (48) \end{matrix}$ where h_(w) is the vertical length (or height) of the conductor and a is the radius (in mks units). As with the helical coil, the traveling wave phase delay of the vertical feed line conductor can be given by

$\begin{matrix} {{\theta_{y} = {{\beta_{w}h_{w}} = {{\frac{2\;\pi}{\lambda_{w}}h_{w}} = {\frac{2\;\pi}{V_{w}\lambda_{0}}h_{w}}}}},} & (49) \end{matrix}$ where β_(w) is the propagation phase constant for the vertical feed line conductor, h_(w) is the vertical length (or height) of the vertical feed line conductor, V_(w) is the velocity factor on the wire, λ₀ is the wavelength at the supplied frequency, and λ_(w) is the propagation wavelength resulting from the velocity factor V_(w). For a uniform cylindrical conductor, the velocity factor is a constant with V_(w)≈0.94, or in a range from about 0.93 to about 0.98. If the mast is considered to be a uniform transmission line, its average characteristic impedance can be approximated by

$\begin{matrix} {{Z_{w} = {\frac{60}{V_{w}}\left\lbrack {{\ln\left( \frac{h_{w}}{a} \right)} - 1} \right\rbrack}},} & (50) \end{matrix}$ where V_(w)≈0.94 for a uniform cylindrical conductor and a is the radius of the conductor. An alternative expression that has been employed in amateur radio literature for the characteristic impedance of a single-wire feed line can be given by

$\begin{matrix} {Z_{w} = {138\;{{\log\left( \frac{1.123\; V_{w}\lambda_{0}}{2\;\pi\; a} \right)}.}}} & (51) \end{matrix}$ Equation (51) implies that Z_(w) for a single-wire feeder varies with frequency. The phase delay can be determined based upon the capacitance and characteristic impedance.

The coil 215 is one example of a phase delay circuit that may be employed as part of the feed network 209. It is understood that other components may be used in the place of the coil 215 as a phase delay circuit in a given embodiment. Such alternative phase delay circuits comprise circuits that provide for a transmission line delay. Such elements provide for the phase delay associated with transmission lines. Accordingly, other examples of phase delay circuits may include sections of transmission lines, circuits that mimic transmission lines such as L-C circuits, sections of coaxial cable or other cables, active circuits that employ operational amplifiers and the like, and other phase delay circuits. It should be noted that whenever an embodiment of a guided surface waveguide probe is discussed herein that includes the use of a coil as phase delay circuit, it is understood that the coil is cited as an example of a phase delay circuit and that other types of phase delay circuits may also be used.

With a charge terminal T₁ positioned over the lossy conducting medium 203 as shown in FIG. 3, the feed network 209 can be adjusted to excite the charge terminal T₁ with the phase shift (Φ) of the complex effective height (h_(eff)) equal to the angle (Ψ) of the wave tilt at the Hankel crossover distance, or Φ=Ψ. When this condition is met, the electric field produced by the charge oscillating Q₁ on the charge terminal T₁ is coupled into a guided surface waveguide mode traveling along the surface of a lossy conducting medium 203. For example, if the Brewster angle (θ_(i,B)), the phase delay (θ_(y)) associated with the vertical feed line conductor 221 (FIG. 7), and the configuration of the coil 215 (FIG. 7) are known, then the position of the tap 224 (FIG. 7) can be determined and adjusted to impose an oscillating charge Q₁ on the charge terminal T₁ with phase Φ=Ψ. The position of the tap 224 may be adjusted to maximize coupling the traveling surface waves into the guided surface waveguide mode. Excess coil length beyond the position of the tap 224 can be removed to reduce the capacitive effects. The vertical wire height and/or the geometrical parameters of the helical coil may also be varied.

The coupling to the guided surface waveguide mode on the surface of the lossy conducting medium 203 can be improved and/or optimized by tuning the guided surface waveguide probe 200 for standing wave resonance with respect to a complex image plane associated with the charge Q₁ on the charge terminal T₁. By doing this, the performance of the guided surface waveguide probe 200 can be adjusted for increased and/or maximum voltage (and thus charge Q₁) on the charge terminal T₁. Referring back to FIG. 3, the effect of the lossy conducting medium 203 in Region 1 can be examined using image theory analysis.

Physically, an elevated charge Q₁ placed over a perfectly conducting plane attracts the free charge on the perfectly conducting plane, which then “piles up” in the region under the elevated charge Q₁. The resulting distribution of “bound” electricity on the perfectly conducting plane is similar to a bell-shaped curve. The superposition of the potential of the elevated charge Q₁, plus the potential of the induced “piled up” charge beneath it, forces a zero equipotential surface for the perfectly conducting plane. The boundary value problem solution that describes the fields in the region above the perfectly conducting plane may be obtained using the classical notion of image charges, where the field from the elevated charge is superimposed with the field from a corresponding “image” charge below the perfectly conducting plane.

This analysis may also be used with respect to a lossy conducting medium 203 by assuming the presence of an effective image charge Q₁′ beneath the guided surface waveguide probe 200. The effective image charge Q₁′ coincides with the charge Q₁ on the charge terminal T₁ about a conducting image ground plane 130, as illustrated in FIG. 3. However, the image charge Q₁′ is not merely located at some real depth and 180° out of phase with the primary source charge Q₁ on the charge terminal T₁, as they would be in the case of a perfect conductor. Rather, the lossy conducting medium 203 (e.g., a terrestrial medium) presents a phase shifted image. That is to say, the image charge Q₁′ is at a complex depth below the surface (or physical boundary) of the lossy conducting medium 203. For a discussion of complex image depth, reference is made to Wait, J. R., “Complex Image Theory—Revisited,” IEEE Antennas and Propagation Magazine, Vol. 33, No. 4, August 1991, pp. 27-29, which is incorporated herein by reference in its entirety.

Instead of the image charge Q₁′ being at a depth that is equal to the physical height (H₁) of the charge Q₁, the conducting image ground plane 130 (representing a perfect conductor) is located at a complex depth of z=−d/2 and the image charge Q₁′ appears at a complex depth (i.e., the “depth” has both magnitude and phase), given by −D₁=−(d/2+d/2+H₁)≠H₁. For vertically polarized sources over the Earth,

$\begin{matrix} {{d = {{\frac{2\sqrt{\gamma_{e}^{2} + k_{0}^{2}}}{\gamma_{e}^{2}} \approx \frac{2}{\gamma_{e}}} = {{d_{r} + {j\; d_{i}}} = {{d}{\angle\zeta}}}}},} & (52) \\ {where} & \; \\ {{\gamma_{e}^{2} = {{j\;\omega\;\mu_{1}\sigma_{1}} - {\omega^{2}\mu_{1}ɛ_{1}}}},{and}} & (53) \\ {{k_{o} = {\omega\sqrt{\mu_{o}ɛ_{o}}}},} & (54) \end{matrix}$ as indicated in Equation (12). The complex spacing of the image charge, in turn, implies that the external field will experience extra phase shifts not encountered when the interface is either a dielectric or a perfect conductor. In the lossy conducting medium, the wave front normal is parallel to the tangent of the conducting image ground plane 130 at z=−d/2, and not at the boundary interface between Regions 1 and 2.

Consider the case illustrated in FIG. 8A where the lossy conducting medium 203 is a finitely conducting Earth 133 with a physical boundary 136. The finitely conducting Earth 133 may be replaced by a perfectly conducting image ground plane 139 as shown in FIG. 8B, which is located at a complex depth z₁ below the physical boundary 136. This equivalent representation exhibits the same impedance when looking down into the interface at the physical boundary 136. The equivalent representation of FIG. 8B can be modeled as an equivalent transmission line, as shown in FIG. 8C. The cross-section of the equivalent structure is represented as a (z-directed) end-loaded transmission line, with the impedance of the perfectly conducting image plane being a short circuit (z_(s)=0). The depth z₁ can be determined by equating the TEM wave impedance looking down at the Earth to an image ground plane impedance z_(in) seen looking into the transmission line of FIG. 8C.

In the case of FIG. 8A, the propagation constant and wave intrinsic impedance in the upper region (air) 142 are

$\begin{matrix} {{\gamma_{o} = {{j\;\omega\sqrt{\mu_{o}ɛ_{o}}} = {0 + {j\;\beta_{o}}}}},{and}} & (55) \\ {z_{o} = {\frac{j\;\omega\;\mu_{o}}{\gamma_{o}} = {\sqrt{\frac{\mu_{o}}{ɛ_{o}}}.}}} & (56) \end{matrix}$ In the lossy Earth 133, the propagation constant and wave intrinsic impedance are

$\begin{matrix} {{\gamma_{e} = \sqrt{j\;\omega\;{\mu_{1}\left( {\sigma_{1} + {j\;\omega\; ɛ_{1}}} \right)}}},{and}} & (57) \\ {Z_{w} = {\frac{j\;\omega\;\mu_{1}}{\gamma_{e}}.}} & (58) \end{matrix}$ For normal incidence, the equivalent representation of FIG. 8B is equivalent to a TEM transmission line whose characteristic impedance is that of air (z_(o)), with propagation constant of γ_(o), and whose length is z₁. As such, the image ground plane impedance Z_(in) seen at the interface for the shorted transmission line of FIG. 8C is given by Z _(in) =Z _(o) tan h(γ_(o) z ₁).  (59) Equating the image ground plane impedance Z_(in) associated with the equivalent model of FIG. 8C to the normal incidence wave impedance of FIG. 8A and solving for z₁ gives the distance to a short circuit (the perfectly conducting image ground plane 139) as

$\begin{matrix} {{z_{1} = {{\frac{1}{\gamma_{o}}{\tanh^{- 1}\left( \frac{z_{e}}{z_{o}} \right)}} = {{\frac{1}{\gamma_{o}}{\tanh^{- 1}\left( \frac{\gamma_{o}}{\gamma_{e}} \right)}} \approx \frac{1}{\gamma_{e}}}}},} & (60) \end{matrix}$ where only the first term of the series expansion for the inverse hyperbolic tangent is considered for this approximation. Note that in the air region 142, the propagation constant is γ_(o)=jβ_(o), so Z_(in)=jZ_(o) tan β_(o)z₁ (which is a purely imaginary quantity for a real z₁), but z_(e) is a complex value if σ≠0. Therefore, Z_(in)=Z_(e) only when z₁ is a complex distance.

Since the equivalent representation of FIG. 8B includes a perfectly conducting image ground plane 139, the image depth for a charge or current lying at the surface of the Earth (physical boundary 136) is equal to distance z₁ on the other side of the image ground plane 139, or d=2×z₁ beneath the Earth's surface (which is located at z=0). Thus, the distance to the perfectly conducting image ground plane 139 can be approximated by

$\begin{matrix} {d = {{2\; z_{1}} \approx {\frac{2}{\gamma_{e}}.}}} & (61) \end{matrix}$ Additionally, the “image charge” will be “equal and opposite” to the real charge, so the potential of the perfectly conducting image ground plane 139 at depth z₁=−d/2 will be zero.

If a charge Q₁ is elevated a distance H₁ above the surface of the Earth as illustrated in FIG. 3, then the image charge Q₁′ resides at a complex distance of D₁=d+H₁ below the surface, or a complex distance of d/2+H₁ below the image ground plane 130. The guided surface waveguide probe 200 b of FIG. 7 can be modeled as an equivalent single-wire transmission line image plane model that can be based upon the perfectly conducting image ground plane 139 of FIG. 8B. FIG. 9A shows an example of the equivalent single-wire transmission line image plane model, and FIG. 9B illustrates an example of the equivalent classic transmission line model, including the shorted transmission line of FIG. 8C.

In the equivalent image plane models of FIGS. 9A and 9B, Φ=θ_(y)+θ_(c) is the traveling wave phase delay of the guided surface waveguide probe 200 referenced to Earth 133 (or the lossy conducting medium 203), θ_(c)=β_(p)H is the electrical length of the coil 215 (FIG. 7), of physical length H, expressed in degrees, θ_(y)=β_(w)h_(w) is the electrical length of the vertical feed line conductor 221 (FIG. 7), of physical length h_(w), expressed in degrees, and θ_(d)=β_(o) d/2 is the phase shift between the image ground plane 139 and the physical boundary 136 of the Earth 133 (or lossy conducting medium 203). In the example of FIGS. 9A and 9B, Z_(w) is the characteristic impedance of the elevated vertical feed line conductor 221 in ohms, Z_(c) is the characteristic impedance of the coil 215 in ohms, and Z_(O) is the characteristic impedance of free space.

At the base of the guided surface waveguide probe 200, the impedance seen “looking up” into the structure is Z_(↑)=Z_(base). With a load impedance of:

$\begin{matrix} {{Z_{L} = \frac{1}{j\;\omega\; C_{T}}},} & (62) \end{matrix}$ where C_(T) is the self-capacitance of the charge terminal T₁, the impedance seen “looking up” into the vertical feed line conductor 221 (FIG. 7) is given by:

$\begin{matrix} {{Z_{2} = {{Z_{W}\frac{Z_{L} + {Z_{w}{\tanh\left( {j\;\beta_{w}h_{w}} \right)}}}{Z_{w} + {Z_{L}{\tanh\left( {j\;\beta_{w}h_{w}} \right)}}}} = {Z_{W}\frac{Z_{L} + {Z_{w}{\tanh\left( {j\;\theta_{y}} \right)}}}{Z_{w} + {Z_{L}{\tanh\left( {j\;\theta_{y}} \right)}}}}}},} & (63) \end{matrix}$ and the impedance seen “looking up” into the coil 215 (FIG. 7) is given by:

$\begin{matrix} {Z_{base} = {{Z_{c}\frac{Z_{2} + {Z_{c}{\tanh\left( {j\;\beta_{p}H} \right)}}}{Z_{c} + {Z_{2}{\tanh\left( {j\;\beta_{p}H} \right)}}}} = {Z_{c}{\frac{Z_{2} + {Z_{c}{\tanh\left( {j\;\theta_{c}} \right)}}}{Z_{c} + {Z_{2}{\tanh\left( {j\;\theta_{c}} \right)}}}.}}}} & (64) \end{matrix}$ At the base of the guided surface waveguide probe 200, the impedance seen “looking down” into the lossy conducting medium 203 is Z_(↓)=Z_(in), which is given by:

$\begin{matrix} {{Z_{in} = {{Z_{o}\frac{Z_{s} + {Z_{o}{\tanh\left\lbrack {j\;{\beta_{o}\left( {d/2} \right)}} \right\rbrack}}}{Z_{o} + {Z_{s}{\tanh\left\lbrack {j\;{\beta_{o}\left( {d/2} \right)}} \right\rbrack}}}} = {Z_{o}{\tanh\left( {j\;\theta_{d}} \right)}}}},} & (65) \end{matrix}$ where Z_(s)=0.

Neglecting losses, the equivalent image plane model can be tuned to resonance when Z_(↓)+Z_(↑)=0 at the physical boundary 136. Or, in the low loss case, X_(↓)+X_(T↑)=0 at the physical boundary 136, where X is the corresponding reactive component. Thus, the impedance at the physical boundary 136 “looking up” into the guided surface waveguide probe 200 is the conjugate of the impedance at the physical boundary 136 “looking down” into the lossy conducting medium 203. By adjusting the load impedance Z_(L) of the charge terminal T₁ while maintaining the traveling wave phase delay Φ equal to the angle of the media's wave tilt Ψ, so that Φ=Ψ, which improves and/or maximizes coupling of the probe's electric field to a guided surface waveguide mode along the surface of the lossy conducting medium 203 (e.g., Earth), the equivalent image plane models of FIGS. 9A and 9B can be tuned to resonance with respect to the image ground plane 139. In this way, the impedance of the equivalent complex image plane model is purely resistive, which maintains a superposed standing wave on the probe structure that maximizes the voltage and elevated charge on terminal T₁, and by equations (1)-(3) and (16) maximizes the propagating surface wave.

It follows from the Hankel solutions, that the guided surface wave excited by the guided surface waveguide probe 200 is an outward propagating traveling wave. The source distribution along the feed network 209 between the charge terminal T₁ and the ground stake 218 of the guided surface waveguide probe 200 (FIGS. 3 and 7) is actually composed of a superposition of a traveling wave plus a standing wave on the structure. With the charge terminal T₁ positioned at or above the physical height h_(p), the phase delay of the traveling wave moving through the feed network 209 is matched to the angle of the wave tilt associated with the lossy conducting medium 203. This mode-matching allows the traveling wave to be launched along the lossy conducting medium 203. Once the phase delay has been established for the traveling wave, the load impedance Z_(L) of the charge terminal T₁ is adjusted to bring the probe structure into standing wave resonance with respect to the image ground plane (130 of FIG. 3 or 139 of FIG. 8), which is at a complex depth of −d/2. In that case, the impedance seen from the image ground plane has zero reactance and the charge on the charge terminal T₁ is maximized.

The distinction between the traveling wave phenomenon and standing wave phenomena is that (1) the phase delay of traveling waves (θ=βd) on a section of transmission line of length d (sometimes called a “delay line”) is due to propagation time delays; whereas (2) the position-dependent phase of standing waves (which are composed of forward and backward propagating waves) depends on both the line length propagation time delay and impedance transitions at interfaces between line sections of different characteristic impedances. In addition to the phase delay that arises due to the physical length of a section of transmission line operating in sinusoidal steady-state, there is an extra reflection coefficient phase at impedance discontinuities that is due to the ratio of Z_(oa)/Z_(ob), where Z_(oa) and Z_(ob) are the characteristic impedances of two sections of a transmission line such as, e.g., a helical coil section of characteristic impedance Z_(oa)=Z_(c) (FIG. 9B) and a straight section of vertical feed line conductor of characteristic impedance Z_(ob)=Z_(w) (FIG. 9B).

As a result of this phenomenon, two relatively short transmission line sections of widely differing characteristic impedance may be used to provide a very large phase shift. For example, a probe structure composed of two sections of transmission line, one of low impedance and one of high impedance, together totaling a physical length of, say, 0.05λ, may be fabricated to provide a phase shift of 90° which is equivalent to a 0.25λ resonance. This is due to the large jump in characteristic impedances. In this way, a physically short probe structure can be electrically longer than the two physical lengths combined. This is illustrated in FIGS. 9A and 9B, where the discontinuities in the impedance ratios provide large jumps in phase. The impedance discontinuity provides a substantial phase shift where the sections are joined together.

Referring to FIG. 10, shown is a flow chart 150 illustrating an example of adjusting a guided surface waveguide probe 200 (FIGS. 3 and 7) to substantially mode-match to a guided surface waveguide mode on the surface of the lossy conducting medium, which launches a guided surface traveling wave along the surface of a lossy conducting medium 203 (FIG. 3). Beginning with 153, the charge terminal T₁ of the guided surface waveguide probe 200 is positioned at a defined height above a lossy conducting medium 203. Utilizing the characteristics of the lossy conducting medium 203 and the operating frequency of the guided surface waveguide probe 200, the Hankel crossover distance can also be found by equating the magnitudes of Equations (20b) and (21) for −jγρ, and solving for R_(x) as illustrated by FIG. 4. The complex index of refraction (n) can be determined using Equation (41), and the complex Brewster angle (θ_(i,B)) can then be determined from Equation (42). The physical height (h_(p)) of the charge terminal T₁ can then be determined from Equation (44). The charge terminal T₁ should be at or higher than the physical height (h_(p)) in order to excite the far-out component of the Hankel function. This height relationship is initially considered when launching surface waves. To reduce or minimize the bound charge on the charge terminal T₁, the height should be at least four times the spherical diameter (or equivalent spherical diameter) of the charge terminal T₁.

At 156, the electrical phase delay Φ of the elevated charge Q₁ on the charge terminal T₁ is matched to the complex wave tilt angle Ψ. The phase delay (θ_(c)) of the helical coil and/or the phase delay (θ_(y)) of the vertical feed line conductor can be adjusted to make Φ equal to the angle (Ψ) of the wave tilt (W). Based on Equation (31), the angle (Ψ) of the wave tilt can be determined from:

$\begin{matrix} {W = {\frac{E_{\rho}}{E_{z}} = {\frac{1}{\tan\mspace{11mu}\theta_{i,B}} = {\frac{1}{n} = {{W}{e^{j\;\Psi}.}}}}}} & (66) \end{matrix}$ The electrical phase Φ can then be matched to the angle of the wave tilt. This angular (or phase) relationship is next considered when launching surface waves. For example, the electrical phase delay Φ=θ_(c)+θ_(y) can be adjusted by varying the geometrical parameters of the coil 215 (FIG. 7) and/or the length (or height) of the vertical feed line conductor 221 (FIG. 7). By matching Φ=Ψ, an electric field can be established at or beyond the Hankel crossover distance (R_(x)) with a complex Brewster angle at the boundary interface to excite the surface waveguide mode and launch a traveling wave along the lossy conducting medium 203.

Next at 159, the load impedance of the charge terminal T₁ is tuned to resonate the equivalent image plane model of the guided surface waveguide probe 200. The depth (d/2) of the conducting image ground plane 139 of FIGS. 9A and 9B (or 130 of FIG. 3) can be determined using Equations (52), (53) and (54) and the values of the lossy conducting medium 203 (e.g., the Earth), which can be measured. Using that depth, the phase shift (θ_(d)) between the image ground plane 139 and the physical boundary 136 of the lossy conducting medium 203 can be determined using θ_(d)=β_(o) d/2. The impedance (Z_(in)) as seen “looking down” into the lossy conducting medium 203 can then be determined using Equation (65). This resonance relationship can be considered to maximize the launched surface waves.

Based upon the adjusted parameters of the coil 215 and the length of the vertical feed line conductor 221, the velocity factor, phase delay, and impedance of the coil 215 and vertical feed line conductor 221 can be determined using Equations (45) through (51). In addition, the self-capacitance (C_(T)) of the charge terminal T₁ can be determined using, e.g., Equation (24). The propagation factor (β_(p)) of the coil 215 can be determined using Equation (35) and the propagation phase constant (β_(w)) for the vertical feed line conductor 221 can be determined using Equation (49). Using the self-capacitance and the determined values of the coil 215 and vertical feed line conductor 221, the impedance (Z_(base)) of the guided surface waveguide probe 200 as seen “looking up” into the coil 215 can be determined using Equations (62), (63) and (64).

The equivalent image plane model of the guided surface waveguide probe 200 can be tuned to resonance by adjusting the load impedance Z_(L) such that the reactance component X_(base) Of Z_(base) cancels out the reactance component X_(in) of Z_(in), or X_(base) X_(in)=0. Thus, the impedance at the physical boundary 136 “looking up” into the guided surface waveguide probe 200 is the conjugate of the impedance at the physical boundary 136 “looking down” into the lossy conducting medium 203. The load impedance Z_(L) can be adjusted by varying the capacitance (C_(T)) of the charge terminal T₁ without changing the electrical phase delay Φ=θ_(c)+θ_(y) of the charge terminal T₁. An iterative approach may be taken to tune the load impedance Z_(L) for resonance of the equivalent image plane model with respect to the conducting image ground plane 139 (or 130). In this way, the coupling of the electric field to a guided surface waveguide mode along the surface of the lossy conducting medium 203 (e.g., Earth) can be improved and/or maximized.

This may be better understood by illustrating the situation with a numerical example. Consider a guided surface waveguide probe 200 comprising a top-loaded vertical stub of physical height h_(p) with a charge terminal T₁ at the top, where the charge terminal T₁ is excited through a helical coil and vertical feed line conductor at an operational frequency (f_(o)) of 1.85 MHz. With a height (H₁) of 16 feet and the lossy conducting medium 203 (e.g., Earth) having a relative permittivity of ε_(r)=15 and a conductivity of σ₁=0.010 mhos/m, several surface wave propagation parameters can be calculated for f_(o)=1.850 MHz. Under these conditions, the Hankel crossover distance can be found to be R_(x)=54.5 feet with a physical height of h_(p)=5.5 feet, which is well below the actual height of the charge terminal T₁. While a charge terminal height of H₁=5.5 feet could have been used, the taller probe structure reduced the bound capacitance, permitting a greater percentage of free charge on the charge terminal T₁ providing greater field strength and excitation of the traveling wave.

The wave length can be determined as:

$\begin{matrix} {{\lambda_{o} = {\frac{c}{f_{o}} = {162.162\mspace{14mu}{meters}}}},} & (67) \end{matrix}$ where c is the speed of light. The complex index of refraction is: n=√{square root over (ε_(r) −jx)}=7.529−j6.546,  (68) from Equation (41), where x=σ₁/ωε_(o) with ω=2πf_(o), and the complex Brewster angle is: θ_(i,B)=arctan(√{square root over (ε_(r) −jx)})=85.6−j3.744°.  (69) from Equation (42). Using Equation (66), the wave tilt values can be determined to be:

$\begin{matrix} {W = {\frac{1}{\tan\mspace{11mu}\theta_{i,B}} = {\frac{1}{n} = {{{W}e^{j\;\Psi}} = {0.101{e^{j\; 40.614{^\circ}}.}}}}}} & (70) \end{matrix}$ Thus, the helical coil can be adjusted to match Φ=Ψ=40.614°

The velocity factor of the vertical feed line conductor (approximated as a uniform cylindrical conductor with a diameter of 0.27 inches) can be given as V_(w)≈0.93. Since h_(p)<<λ_(o), the propagation phase constant for the vertical feed line conductor can be approximated as:

$\begin{matrix} {\beta_{w} = {\frac{2\pi}{\lambda_{w}} = {\frac{2\pi}{V_{w}\lambda_{0}} = {0.042\mspace{14mu}{m^{- 1}.}}}}} & (71) \end{matrix}$ From Equation (49) the phase delay of the vertical feed line conductor is: θ_(y)=β_(w) h _(w)≈β_(w) h _(p)=11.640°.  (72) By adjusting the phase delay of the helical coil so that θ_(c)=28.974°=40.614°−11.640°, Φ will equal Ψ to match the guided surface waveguide mode. To illustrate the relationship between Φ and Ψ, FIG. 11 shows a plot of both over a range of frequencies. As both Φ and Ψ are frequency dependent, it can be seen that their respective curves cross over each other at approximately 1.85 MHz.

For a helical coil having a conductor diameter of 0.0881 inches, a coil diameter (D) of 30 inches and a turn-to-turn spacing (s) of 4 inches, the velocity factor for the coil can be determined using Equation (45) as:

$\begin{matrix} {{{V_{f} = {\frac{1}{\sqrt{1 + {20\left( \frac{D}{s} \right)^{2.5}\left( \frac{D}{\lambda_{o}} \right)^{0.5}}}} = 0.069}},}\;} & (73) \end{matrix}$ and the propagation factor from Equation (35) is:

$\begin{matrix} {\beta_{p} = {\frac{2\pi}{V_{f}\lambda_{0}} = {0.564\mspace{14mu}{m^{- 1}.}}}} & (74) \end{matrix}$ With θ_(c)=28.974°, the axial length of the solenoidal helix (H) can be determined using Equation (46) such that:

$\begin{matrix} {H = {\frac{\theta_{c}}{\beta_{p}} = {35.2732\mspace{14mu}{{inches}.}}}} & (75) \end{matrix}$ This height determines the location on the helical coil where the vertical feed line conductor is connected, resulting in a coil with 8.818 turns (N=H/s).

With the traveling wave phase delay of the coil and vertical feed line conductor adjusted to match the wave tilt angle (Φ=θ_(c)+θ_(y)=Ψ), the load impedance (Z_(L)) of the charge terminal T₁ can be adjusted for standing wave resonance of the equivalent image plane model of the guided surface wave probe 200. From the measured permittivity, conductivity and permeability of the Earth, the radial propagation constant can be determined using Equation (57) γ_(e)=√{square root over (jωu ₁(σ₁ +jωε ₁))}=0.25+j0.292 m⁻¹,  (76) And the complex depth of the conducting image ground plane can be approximated from Equation (52) as:

$\begin{matrix} {{{d \approx \frac{2}{\gamma_{e}}} = {3.364 + {j\mspace{11mu} 3.963\mspace{14mu}{meters}}}},} & (77) \end{matrix}$ with a corresponding phase shift between the conducting image ground plane and the physical boundary of the Earth given by: θ_(d)=β_(o)(d/2)=4.015−j4.73°.  (78) Using Equation (65), the impedance seen “looking down” into the lossy conducting medium 203 (i.e., Earth) can be determined as: Z _(in) =Z _(o) tan h(jθ _(d))=R _(in) +jX _(in)=31.191+j26.27 ohms.  (79)

By matching the reactive component (X_(in)) seen “looking down” into the lossy conducting medium 203 with the reactive component (X_(base)) seen “looking up” into the guided surface wave probe 200, the coupling into the guided surface waveguide mode may be maximized. This can be accomplished by adjusting the capacitance of the charge terminal T₁ without changing the traveling wave phase delays of the coil and vertical feed line conductor. For example, by adjusting the charge terminal capacitance (C_(T)) to 61.8126 pF, the load impedance from Equation (62) is:

$\begin{matrix} {{Z_{L} = {\frac{1}{j\;\omega\; C_{T}} = {{- j}\mspace{11mu} 1392\mspace{14mu}{ohms}}}},} & (80) \end{matrix}$ and the reactive components at the boundary are matched.

Using Equation (51), the impedance of the vertical feed line conductor (having a diameter (2a) of 0.27 inches) is given as

$\begin{matrix} {{{Z_{w} - {138\mspace{14mu}{\log\left( \frac{1.123\mspace{14mu} V_{w}\lambda_{0}}{2\pi\; a} \right)}}} = {537.534\mspace{14mu}{ohms}}},} & (81) \end{matrix}$ and the impedance seen “looking up” into the vertical feed line conductor is given by Equation (63) as:

$\begin{matrix} {Z_{2} = {{Z_{W}\frac{Z_{L} + {Z_{W}{\tanh\left( {j\;\theta_{y}} \right)}}}{Z_{W} + {Z_{L}{\tanh\left( {j\;\theta_{y}} \right)}}}} = {{- j}\mspace{11mu} 835.438\mspace{14mu}{{ohms}.}}}} & (82) \end{matrix}$ Using Equation (47), the characteristic impedance of the helical coil is given as

$\begin{matrix} {{Z_{c} = {{\frac{60}{V_{f}}\left\lbrack {{\ln\left( \frac{V_{f}\lambda_{0}}{D} \right)} - 1.027} \right\rbrack} = {1446\mspace{14mu}{ohms}}}},} & (83) \end{matrix}$ and the impedance seen “looking up” into the coil at the base is given by Equation (64) as:

$\begin{matrix} {Z_{base} = {{Z_{c}\frac{Z_{2} + {Z_{c}{\tanh\left( {j\;\theta_{c}} \right)}}}{Z_{c} + {Z_{2}{\tanh\left( {j\;\theta_{c}} \right)}}}} = {{- j}\mspace{11mu} 26.271\mspace{14mu}{{ohms}.}}}} & (84) \end{matrix}$ When compared to the solution of Equation (79), it can be seen that the reactive components are opposite and approximately equal, and thus are conjugates of each other. Thus, the impedance (Z_(ip)) seen “looking up” into the equivalent image plane model of FIGS. 9A and 9B from the perfectly conducting image ground plane is only resistive or Z_(ip)=R+j0.

When the electric fields produced by a guided surface waveguide probe 200 (FIG. 3) are established by matching the traveling wave phase delay of the feed network to the wave tilt angle and the probe structure is resonated with respect to the perfectly conducting image ground plane at complex depth z=−d/2, the fields are substantially mode-matched to a guided surface waveguide mode on the surface of the lossy conducting medium, a guided surface traveling wave is launched along the surface of the lossy conducting medium. As illustrated in FIG. 1, the guided field strength curve 103 of the guided electromagnetic field has a characteristic exponential decay of e^(−αd)/√{square root over (d)} and exhibits a distinctive knee 109 on the log-log scale.

In summary, both analytically and experimentally, the traveling wave component on the structure of the guided surface waveguide probe 200 has a phase delay (Φ) at its upper terminal that matches the angle (Ψ) of the wave tilt of the surface traveling wave (Φ=Ψ). Under this condition, the surface waveguide may be considered to be “mode-matched”. Furthermore, the resonant standing wave component on the structure of the guided surface waveguide probe 200 has a V_(MAX) at the charge terminal T₁ and a V_(MIN) down at the image plane 139 (FIG. 8B) where Z_(ip)=R_(ip)+j 0 at a complex depth of z=−d/2, not at the connection at the physical boundary 136 of the lossy conducting medium 203 (FIG. 8B). Lastly, the charge terminal T₁ is of sufficient height H₁ of FIG. 3 (h≥R_(x) tan ψ_(i,B)) so that electromagnetic waves incident onto the lossy conducting medium 203 at the complex Brewster angle do so out at a distance (≥R_(x)) where the 1/√{square root over (r)} term is predominant. Receive circuits can be utilized with one or more guided surface waveguide probes to facilitate wireless transmission and/or power delivery systems.

Referring back to FIG. 3, operation of a guided surface waveguide probe 200 may be controlled to adjust for variations in operational conditions associated with the guided surface waveguide probe 200. For example, an adaptive probe control system 230 can be used to control the feed network 209 and/or the charge terminal T₁ to control the operation of the guided surface waveguide probe 200. Operational conditions can include, but are not limited to, variations in the characteristics of the lossy conducting medium 203 (e.g., conductivity σ and relative permittivity ε_(r)), variations in field strength and/or variations in loading of the guided surface waveguide probe 200. As can be seen from Equations (31), (41) and (42), the index of refraction (n), the complex Brewster angle (θ_(i,B)), and the wave tilt (|W|e^(jΨ)) can be affected by changes in soil conductivity and permittivity resulting from, e.g., weather conditions.

Equipment such as, e.g., conductivity measurement probes, permittivity sensors, ground parameter meters, field meters, current monitors and/or load receivers can be used to monitor for changes in the operational conditions and provide information about current operational conditions to the adaptive probe control system 230. The probe control system 230 can then make one or more adjustments to the guided surface waveguide probe 200 to maintain specified operational conditions for the guided surface waveguide probe 200. For instance, as the moisture and temperature vary, the conductivity of the soil will also vary. Conductivity measurement probes and/or permittivity sensors may be located at multiple locations around the guided surface waveguide probe 200. Generally, it would be desirable to monitor the conductivity and/or permittivity at or about the Hankel crossover distance R_(x) for the operational frequency. Conductivity measurement probes and/or permittivity sensors may be located at multiple locations (e.g., in each quadrant) around the guided surface waveguide probe 200.

The conductivity measurement probes and/or permittivity sensors can be configured to evaluate the conductivity and/or permittivity on a periodic basis and communicate the information to the probe control system 230. The information may be communicated to the probe control system 230 through a network such as, but not limited to, a LAN, WLAN, cellular network, or other appropriate wired or wireless communication network. Based upon the monitored conductivity and/or permittivity, the probe control system 230 may evaluate the variation in the index of refraction (n), the complex Brewster angle (θ_(i,B)), and/or the wave tilt (|W|e^(jΨ)) and adjust the guided surface waveguide probe 200 to maintain the phase delay (Φ) of the feed network 209 equal to the wave tilt angle (Ψ) and/or maintain resonance of the equivalent image plane model of the guided surface waveguide probe 200. This can be accomplished by adjusting, e.g., θ_(y), θ_(c) and/or C_(T). For instance, the probe control system 230 can adjust the self-capacitance of the charge terminal T₁ and/or the phase delay (θ_(y), θ_(c)) applied to the charge terminal T₁ to maintain the electrical launching efficiency of the guided surface wave at or near its maximum. For example, the self-capacitance of the charge terminal T₁ can be varied by changing the size of the terminal. The charge distribution can also be improved by increasing the size of the charge terminal T₁, which can reduce the chance of an electrical discharge from the charge terminal T₁. In other embodiments, the charge terminal T₁ can include a variable inductance that can be adjusted to change the load impedance Z_(L). The phase applied to the charge terminal T₁ can be adjusted by varying the tap position on the coil 215 (FIG. 7), and/or by including a plurality of predefined taps along the coil 215 and switching between the different predefined tap locations to maximize the launching efficiency.

Field or field strength (FS) meters may also be distributed about the guided surface waveguide probe 200 to measure field strength of fields associated with the guided surface wave. The field or FS meters can be configured to detect the field strength and/or changes in the field strength (e.g., electric field strength) and communicate that information to the probe control system 230. The information may be communicated to the probe control system 230 through a network such as, but not limited to, a LAN, WLAN, cellular network, or other appropriate communication network. As the load and/or environmental conditions change or vary during operation, the guided surface waveguide probe 200 may be adjusted to maintain specified field strength(s) at the FS meter locations to ensure appropriate power transmission to the receivers and the loads they supply.

For example, the phase delay (Φ=θ_(y)+θ_(c)) applied to the charge terminal T₁ can be adjusted to match the wave tilt angle (Ψ). By adjusting one or both phase delays, the guided surface waveguide probe 200 can be adjusted to ensure the wave tilt corresponds to the complex Brewster angle. This can be accomplished by adjusting a tap position on the coil 215 (FIG. 7) to change the phase delay supplied to the charge terminal T₁. The voltage level supplied to the charge terminal T₁ can also be increased or decreased to adjust the electric field strength. This may be accomplished by adjusting the output voltage of the excitation source 212 or by adjusting or reconfiguring the feed network 209. For instance, the position of the tap 227 (FIG. 7) for the AC source 212 can be adjusted to increase the voltage seen by the charge terminal Maintaining field strength levels within predefined ranges can improve coupling by the receivers, reduce ground current losses, and avoid interference with transmissions from other guided surface waveguide probes 200.

The probe control system 230 can be implemented with hardware, firmware, software executed by hardware, or a combination thereof. For example, the probe control system 230 can include processing circuitry including a processor and a memory, both of which can be coupled to a local interface such as, for example, a data bus with an accompanying control/address bus as can be appreciated by those with ordinary skill in the art. A probe control application may be executed by the processor to adjust the operation of the guided surface waveguide probe 200 based upon monitored conditions. The probe control system 230 can also include one or more network interfaces for communicating with the various monitoring devices. Communications can be through a network such as, but not limited to, a LAN, WLAN, cellular network, or other appropriate communication network. The probe control system 230 may comprise, for example, a computer system such as a server, desktop computer, laptop, or other system with like capability.

Referring back to the example of FIG. 5A, the complex angle trigonometry is shown for the ray optic interpretation of the incident electric field (E) of the charge terminal T₁ with a complex Brewster angle (θ_(i,B)) at the Hankel crossover distance (R_(x)). Recall that, for a lossy conducting medium, the Brewster angle is complex and specified by equation (38). Electrically, the geometric parameters are related by the electrical effective height (h_(eff)) of the charge terminal T₁ by equation (39). Since both the physical height (h_(p)) and the Hankel crossover distance (R_(x)) are real quantities, the angle of the desired guided surface wave tilt at the Hankel crossover distance (W_(Rx)) is equal to the phase (Φ) of the complex effective height (h_(eff)). With the charge terminal T₁ positioned at the physical height h_(p) and excited with a charge having the appropriate phase Φ, the resulting electric field is incident with the lossy conducting medium boundary interface at the Hankel crossover distance R_(x), and at the Brewster angle. Under these conditions, the guided surface waveguide mode can be excited without reflection or substantially negligible reflection.

However, Equation (39) means that the physical height of the guided surface waveguide probe 200 can be relatively small. While this will excite the guided surface waveguide mode, this can result in an unduly large bound charge with little free charge. To compensate, the charge terminal T₁ can be raised to an appropriate elevation to increase the amount of free charge. As one example rule of thumb, the charge terminal T₁ can be positioned at an elevation of about 4-5 times (or more) the effective diameter of the charge terminal T₁. FIG. 6 illustrates the effect of raising the charge terminal T₁ above the physical height (h_(p)) shown in FIG. 5A. The increased elevation causes the distance at which the wave tilt is incident with the lossy conductive medium to move beyond the Hankel crossover point 121 (FIG. 5A). To improve coupling in the guided surface waveguide mode, and thus provide for a greater launching efficiency of the guided surface wave, a lower compensation terminal T₂ can be used to adjust the total effective height (h_(TE)) of the charge terminal T₁ such that the wave tilt at the Hankel crossover distance is at the Brewster angle.

Referring to FIG. 12, shown is an example of a guided surface waveguide probe 200 c that includes an elevated charge terminal T₁ and a lower compensation terminal T₂ that are arranged along a vertical axis z that is normal to a plane presented by the lossy conducting medium 203. In this respect, the charge terminal T₁ is placed directly above the compensation terminal T₂ although it is possible that some other arrangement of two or more charge and/or compensation terminals T_(N) can be used. The guided surface waveguide probe 200 c is disposed above a lossy conducting medium 203 according to an embodiment of the present disclosure. The lossy conducting medium 203 makes up Region 1 with a second medium 206 that makes up Region 2 sharing a boundary interface with the lossy conducting medium 203.

The guided surface waveguide probe 200 c includes a feed network 209 that couples an excitation source 212 to the charge terminal T₁ and the compensation terminal T₂. According to various embodiments, charges Q₁ and Q₂ can be imposed on the respective charge and compensation terminals T₁ and T₂, depending on the voltages applied to terminals T₁ and T₂ at any given instant. I₁ is the conduction current feeding the charge Q₁ on the charge terminal T₁ via the terminal lead, and I₂ is the conduction current feeding the charge Q₂ on the compensation terminal T₂ via the terminal lead.

According to the embodiment of FIG. 12, the charge terminal T₁ is positioned over the lossy conducting medium 203 at a physical height H₁, and the compensation terminal T₂ is positioned directly below T₁ along the vertical axis z at a physical height H₂, where H₂ is less than H₁. The height h of the transmission structure may be calculated as h=H₁−H₂. The charge terminal T₁ has an isolated (or self) capacitance C₁, and the compensation terminal T₂ has an isolated (or self) capacitance C₂. A mutual capacitance C_(M) can also exist between the terminals T₁ and T₂ depending on the distance therebetween. During operation, charges Q₁ and Q₂ are imposed on the charge terminal T₁ and the compensation terminal T₂, respectively, depending on the voltages applied to the charge terminal T₁ and the compensation terminal T₂ at any given instant.

Referring next to FIG. 13, shown is a ray optics interpretation of the effects produced by the elevated charge Q₁ on charge terminal T₁ and compensation terminal T₂ of FIG. 12. With the charge terminal T₁ elevated to a height where the ray intersects with the lossy conductive medium at the Brewster angle at a distance greater than the Hankel crossover point 121 as illustrated by line 163, the compensation terminal T₂ can be used to adjust h_(TE) by compensating for the increased height. The effect of the compensation terminal T₂ is to reduce the electrical effective height of the guided surface waveguide probe (or effectively raise the lossy medium interface) such that the wave tilt at the Hankel crossover distance is at the Brewster angle as illustrated by line 166.

The total effective height can be written as the superposition of an upper effective height (h_(UE)) associated with the charge terminal T₁ and a lower effective height (h_(LE)) associated with the compensation terminal T₂ such that h _(TE) =h _(UE) +h _(LE) =h _(p) e ^(j(βh) ^(p) ^(+Φ) ^(U) ⁾ +h _(d) e ^(j(βh) ^(d) ^(+Φ) ^(L) ⁾ =R _(x) ×W,  (85) where Φ_(U) is the phase delay applied to the upper charge terminal T₁, Φ_(L) is the phase delay applied to the lower compensation terminal T₂, β=2π/λ_(p) is the propagation factor from Equation (35), h_(p) is the physical height of the charge terminal T₁ and h_(d) is the physical height of the compensation terminal T₂. If extra lead lengths are taken into consideration, they can be accounted for by adding the charge terminal lead length z to the physical height h_(p) of the charge terminal T₁ and the compensation terminal lead length y to the physical height h_(d) of the compensation terminal T₂ as shown in h _(TE)=(h _(p) +z)e ^(j(β(h) ^(p) ^(+z)+Φ) ^(U) ⁾+(h _(d) +y)e ^(j(β(h) ^(d) ^(+y)+Φ) ^(L) ⁾ =R _(x) ×W.  (86) The lower effective height can be used to adjust the total effective height (h_(TE)) to equal the complex effective height (h_(eff)) of FIG. 5A.

Equations (85) or (86) can be used to determine the physical height of the lower disk of the compensation terminal T₂ and the phase angles to feed the terminals in order to obtain the desired wave tilt at the Hankel crossover distance. For example, Equation (86) can be rewritten as the phase shift applied to the charge terminal T₁ as a function of the compensation terminal height (h_(d)) to give

$\begin{matrix} {{\Phi_{U}\left( h_{d} \right)} = {{- {\beta\left( {h_{p} + z} \right)}} - {j\;{{\ln\left( \frac{{R_{x} \times W} - {\left( {h_{d} + y} \right)e^{j{({{\beta\; h_{d}} + {\beta\; y} + \Phi_{L}})}}}}{\left( {h_{p} + z} \right)} \right)}.}}}} & (87) \end{matrix}$

To determine the positioning of the compensation terminal T₂, the relationships discussed above can be utilized. First, the total effective height (h_(TE)) is the superposition of the complex effective height (h_(UE)) of the upper charge terminal T₁ and the complex effective height (h_(LE)) of the lower compensation terminal T₂ as expressed in Equation (86). Next, the tangent of the angle of incidence can be expressed geometrically as

$\begin{matrix} {{{\tan\;\psi_{E}} = \frac{h_{TE}}{R_{x}}},} & (88) \end{matrix}$ which is equal to the definition of the wave tilt, W. Finally, given the desired Hankel crossover distance R_(x), the h_(TE) can be adjusted to make the wave tilt of the incident ray match the complex Brewster angle at the Hankel crossover point 121. This can be accomplished by adjusting h_(p), Φ_(U), and/or h_(d).

These concepts may be better understood when discussed in the context of an example of a guided surface waveguide probe. Referring to FIG. 14, shown is a graphical representation of an example of a guided surface waveguide probe 200 d including an upper charge terminal T₁ (e.g., a sphere at height h_(T)) and a lower compensation terminal T₂ (e.g., a disk at height h_(d)) that are positioned along a vertical axis z that is substantially normal to the plane presented by the lossy conducting medium 203. During operation, charges Q₁ and Q₂ are imposed on the charge and compensation terminals T₁ and T₂, respectively, depending on the voltages applied to the terminals T₁ and T₂ at any given instant.

An AC source 212 acts as the excitation source for the charge terminal T₁, which is coupled to the guided surface waveguide probe 200 d through a feed network 209 comprising a coil 215 such as, e.g., a helical coil. The AC source 212 can be connected across a lower portion of the coil 215 through a tap 227, as shown in FIG. 14, or can be inductively coupled to the coil 215 by way of a primary coil. The coil 215 can be coupled to a ground stake 218 at a first end and the charge terminal T₁ at a second end. In some implementations, the connection to the charge terminal T₁ can be adjusted using a tap 224 at the second end of the coil 215. The compensation terminal T₂ is positioned above and substantially parallel with the lossy conducting medium 203 (e.g., the ground or Earth), and energized through a tap 233 coupled to the coil 215. An ammeter 236 located between the coil 215 and ground stake 218 can be used to provide an indication of the magnitude of the current flow (I₀) at the base of the guided surface waveguide probe. Alternatively, a current clamp may be used around the conductor coupled to the ground stake 218 to obtain an indication of the magnitude of the current flow (I₀).

In the example of FIG. 14, the coil 215 is coupled to a ground stake 218 at a first end and the charge terminal T₁ at a second end via a vertical feed line conductor 221. In some implementations, the connection to the charge terminal T₁ can be adjusted using a tap 224 at the second end of the coil 215 as shown in FIG. 14. The coil 215 can be energized at an operating frequency by the AC source 212 through a tap 227 at a lower portion of the coil 215. In other implementations, the AC source 212 can be inductively coupled to the coil 215 through a primary coil. The compensation terminal T₂ is energized through a tap 233 coupled to the coil 215. An ammeter 236 located between the coil 215 and ground stake 218 can be used to provide an indication of the magnitude of the current flow at the base of the guided surface waveguide probe 200 d. Alternatively, a current clamp may be used around the conductor coupled to the ground stake 218 to obtain an indication of the magnitude of the current flow. The compensation terminal T₂ is positioned above and substantially parallel with the lossy conducting medium 203 (e.g., the ground).

In the example of FIG. 14, the connection to the charge terminal T₁ located on the coil 215 above the connection point of tap 233 for the compensation terminal T₂. Such an adjustment allows an increased voltage (and thus a higher charge Q₁) to be applied to the upper charge terminal T₁. In other embodiments, the connection points for the charge terminal T₁ and the compensation terminal T₂ can be reversed. It is possible to adjust the total effective height (h_(TE)) of the guided surface waveguide probe 200 d to excite an electric field having a guided surface wave tilt at the Hankel crossover distance R_(x). The Hankel crossover distance can also be found by equating the magnitudes of equations (20b) and (21) for −jγρ, and solving for R_(x) as illustrated by FIG. 4. The index of refraction (n), the complex Brewster angle (θ_(i,B) and ψ_(i,B)), the wave tilt (|W|e^(jΨ)) and the complex effective height (h_(eff)=h_(p)e^(jΦ)) can be determined as described with respect to Equations (41)-(44) above.

With the selected charge terminal T₁ configuration, a spherical diameter (or the effective spherical diameter) can be determined. For example, if the charge terminal T₁ is not configured as a sphere, then the terminal configuration may be modeled as a spherical capacitance having an effective spherical diameter. The size of the charge terminal T₁ can be chosen to provide a sufficiently large surface for the charge Q₁ imposed on the terminals. In general, it is desirable to make the charge terminal T₁ as large as practical. The size of the charge terminal T₁ should be large enough to avoid ionization of the surrounding air, which can result in electrical discharge or sparking around the charge terminal. To reduce the amount of bound charge on the charge terminal T₁, the desired elevation to provide free charge on the charge terminal T₁ for launching a guided surface wave should be at least 4-5 times the effective spherical diameter above the lossy conductive medium (e.g., the Earth). The compensation terminal T₂ can be used to adjust the total effective height (h_(TE)) of the guided surface waveguide probe 200 d to excite an electric field having a guided surface wave tilt at R_(x). The compensation terminal T₂ can be positioned below the charge terminal T₁ at h_(d)=h_(T)−h_(p), where h_(T) is the total physical height of the charge terminal T₁. With the position of the compensation terminal T₂ fixed and the phase delay Φ_(U) applied to the upper charge terminal T₁, the phase delay Φ_(L) applied to the lower compensation terminal T₂ can be determined using the relationships of Equation (86), such that:

$\begin{matrix} {{\Phi_{U}\left( h_{d} \right)} = {{- {\beta\left( {h_{d} + y} \right)}} - {j\;{{\ln\left( \frac{{R_{x} \times W} - {\left( {h_{p} + z} \right){\mathbb{e}}^{j{({{\beta\; h_{p}} + {\beta\; z} + \Phi_{L}})}}}}{\left( {h_{d} + y} \right)} \right)}.}}}} & (89) \end{matrix}$ In alternative embodiments, the compensation terminal T₂ can be positioned at a height h_(d) where Im{Φ_(L)}=0. This is graphically illustrated in FIG. 15A, which shows plots 172 and 175 of the imaginary and real parts of Φ_(U), respectively. The compensation terminal T₂ is positioned at a height h_(d) where Im{Φ_(U)}=0, as graphically illustrated in plot 172. At this fixed height, the coil phase Φ_(U) can be determined from Re{Φ_(U)}, as graphically illustrated in plot 175.

With the AC source 212 coupled to the coil 215 (e.g., at the 50Ω point to maximize coupling), the position of tap 233 may be adjusted for parallel resonance of the compensation terminal T₂ with at least a portion of the coil at the frequency of operation. FIG. 15B shows a schematic diagram of the general electrical hookup of FIG. 14 in which V₁ is the voltage applied to the lower portion of the coil 215 from the AC source 212 through tap 227, V₂ is the voltage at tap 224 that is supplied to the upper charge terminal T₁, and V₃ is the voltage applied to the lower compensation terminal T₂ through tap 233. The resistances R_(p) and R_(d) represent the ground return resistances of the charge terminal T₁ and compensation terminal T₂, respectively. The charge and compensation terminals T₁ and T₂ may be configured as spheres, cylinders, toroids, rings, hoods, or any other combination of capacitive structures. The size of the charge and compensation terminals T₁ and T₂ can be chosen to provide a sufficiently large surface for the charges Q₁ and Q₂ imposed on the terminals. In general, it is desirable to make the charge terminal T₁ as large as practical. The size of the charge terminal T₁ should be large enough to avoid ionization of the surrounding air, which can result in electrical discharge or sparking around the charge terminal. The self-capacitance C_(p) and C_(d) of the charge and compensation terminals T₁ and T₂ respectively, can be determined using, for example, equation (24).

As can be seen in FIG. 15B, a resonant circuit is formed by at least a portion of the inductance of the coil 215, the self-capacitance C_(d) of the compensation terminal T₂, and the ground return resistance R_(d) associated with the compensation terminal T₂. The parallel resonance can be established by adjusting the voltage V₃ applied to the compensation terminal T₂ (e.g., by adjusting a tap 233 position on the coil 215) or by adjusting the height and/or size of the compensation terminal T₂ to adjust C_(d). The position of the coil tap 233 can be adjusted for parallel resonance, which will result in the ground current through the ground stake 218 and through the ammeter 236 reaching a maximum point. After parallel resonance of the compensation terminal T₂ has been established, the position of the tap 227 for the AC source 212 can be adjusted to the 50Ω point on the coil 215.

Voltage V₂ from the coil 215 can be applied to the charge terminal T₁, and the position of tap 224 can be adjusted such that the phase (Φ) of the total effective height (h_(TE)) approximately equals the angle of the guided surface wave tilt (W_(Rx)) at the Hankel crossover distance (R_(x)). The position of the coil tap 224 can be adjusted until this operating point is reached, which results in the ground current through the ammeter 236 increasing to a maximum. At this point, the resultant fields excited by the guided surface waveguide probe 200 d are substantially mode-matched to a guided surface waveguide mode on the surface of the lossy conducting medium 203, resulting in the launching of a guided surface wave along the surface of the lossy conducting medium 203. This can be verified by measuring field strength along a radial extending from the guided surface waveguide probe 200.

Resonance of the circuit including the compensation terminal T₂ may change with the attachment of the charge terminal T₁ and/or with adjustment of the voltage applied to the charge terminal T₁ through tap 224. While adjusting the compensation terminal circuit for resonance aids the subsequent adjustment of the charge terminal connection, it is not necessary to establish the guided surface wave tilt (W_(Rx)) at the Hankel crossover distance (R_(x)). The system may be further adjusted to improve coupling by iteratively adjusting the position of the tap 227 for the AC source 212 to be at the 50Ω point on the coil 215 and adjusting the position of tap 233 to maximize the ground current through the ammeter 236. Resonance of the circuit including the compensation terminal T₂ may drift as the positions of taps 227 and 233 are adjusted, or when other components are attached to the coil 215.

In other implementations, the voltage V₂ from the coil 215 can be applied to the charge terminal T₁, and the position of tap 233 can be adjusted such that the phase (Φ) of the total effective height (h_(TE)) approximately equals the angle (Ψ) of the guided surface wave tilt at R_(x). The position of the coil tap 224 can be adjusted until the operating point is reached, resulting in the ground current through the ammeter 236 substantially reaching a maximum. The resultant fields are substantially mode-matched to a guided surface waveguide mode on the surface of the lossy conducting medium 203, and a guided surface wave is launched along the surface of the lossy conducting medium 203. This can be verified by measuring field strength along a radial extending from the guided surface waveguide probe 200. The system may be further adjusted to improve coupling by iteratively adjusting the position of the tap 227 for the AC source 212 to be at the 50Ω point on the coil 215 and adjusting the position of tap 224 and/or 233 to maximize the ground current through the ammeter 236.

Referring back to FIG. 12, operation of a guided surface waveguide probe 200 may be controlled to adjust for variations in operational conditions associated with the guided surface waveguide probe 200. For example, a probe control system 230 can be used to control the feed network 209 and/or positioning of the charge terminal T₁ and/or compensation terminal T₂ to control the operation of the guided surface waveguide probe 200. Operational conditions can include, but are not limited to, variations in the characteristics of the lossy conducting medium 203 (e.g., conductivity σ and relative permittivity ε_(r)), variations in field strength and/or variations in loading of the guided surface waveguide probe 200. As can be seen from Equations (41)-(44), the index of refraction (n), the complex Brewster angle (θ_(i,B) and ψ_(i,B)), the wave tilt (|W|e^(jΨ)) and the complex effective height (h_(eff)=h_(p)e^(jΦ)) can be affected by changes in soil conductivity and permittivity resulting from, e.g., weather conditions.

Equipment such as, e.g., conductivity measurement probes, permittivity sensors, ground parameter meters, field meters, current monitors and/or load receivers can be used to monitor for changes in the operational conditions and provide information about current operational conditions to the probe control system 230. The probe control system 230 can then make one or more adjustments to the guided surface waveguide probe 200 to maintain specified operational conditions for the guided surface waveguide probe 200. For instance, as the moisture and temperature vary, the conductivity of the soil will also vary. Conductivity measurement probes and/or permittivity sensors may be located at multiple locations around the guided surface waveguide probe 200. Generally, it would be desirable to monitor the conductivity and/or permittivity at or about the Hankel crossover distance R_(x) for the operational frequency. Conductivity measurement probes and/or permittivity sensors may be located at multiple locations (e.g., in each quadrant) around the guided surface waveguide probe 200.

With reference then to FIG. 16, shown is an example of a guided surface waveguide probe 200 e that includes a charge terminal T₁ and a charge terminal T₂ that are arranged along a vertical axis z. The guided surface waveguide probe 200 e is disposed above a lossy conducting medium 203, which makes up Region 1. In addition, a second medium 206 shares a boundary interface with the lossy conducting medium 203 and makes up Region 2. The charge terminals T₁ and T₂ are positioned over the lossy conducting medium 203. The charge terminal T₁ is positioned at height H₁, and the charge terminal T₂ is positioned directly below T₁ along the vertical axis z at height H₂, where H₂ is less than H₁. The height h of the transmission structure presented by the guided surface waveguide probe 200 e is h=H₁−H₂. The guided surface waveguide probe 200 e includes a probe feed network 209 that couples an excitation source 212 to the charge terminals T₁ and T₂.

The charge terminals T₁ and/or T₂ include a conductive mass that can hold an electrical charge, which may be sized to hold as much charge as practically possible. The charge terminal T₁ has a self-capacitance C₁, and the charge terminal T₂ has a self-capacitance C₂, which can be determined using, for example, equation (24). By virtue of the placement of the charge terminal T₁ directly above the charge terminal T₂, a mutual capacitance C_(M) is created between the charge terminals T₁ and T₂. Note that the charge terminals T₁ and T₂ need not be identical, but each can have a separate size and shape, and can include different conducting materials. Ultimately, the field strength of a guided surface wave launched by a guided surface waveguide probe 200 e is directly proportional to the quantity of charge on the terminal T₁. The charge Q₁ is, in turn, proportional to the self-capacitance C₁ associated with the charge terminal T₁ since Q₁=C₁V, where V is the voltage imposed on the charge terminal T₁.

When properly adjusted to operate at a predefined operating frequency, the guided surface waveguide probe 200 e generates a guided surface wave along the surface of the lossy conducting medium 203. The excitation source 212 can generate electrical energy at the predefined frequency that is applied to the guided surface waveguide probe 200 e to excite the structure. When the electromagnetic fields generated by the guided surface waveguide probe 200 e are substantially mode-matched with the lossy conducting medium 203, the electromagnetic fields substantially synthesize a wave front incident at a complex Brewster angle that results in little or no reflection. Thus, the surface waveguide probe 200 e does not produce a radiated wave, but launches a guided surface traveling wave along the surface of a lossy conducting medium 203. The energy from the excitation source 212 can be transmitted as Zenneck surface currents to one or more receivers that are located within an effective transmission range of the guided surface waveguide probe 200 e.

One can determine asymptotes of the radial Zenneck surface current J_(ρ)(ρ) on the surface of the lossy conducting medium 203 to be J₁(ρ) close-in and J₂(ρ) far-out, where

$\begin{matrix} {{{{{Close}\text{-}{in}\mspace{14mu}\left( {\rho < {\lambda/8}} \right)\text{:}\mspace{14mu}{J_{\rho}(\rho)}} \sim J_{1}} = {\frac{I_{1} + I_{2}}{2\;\pi\;\rho} + \frac{{E_{\rho}^{QS}\left( Q_{1} \right)} + {E_{\rho}^{QS}\left( Q_{2} \right)}}{Z_{p}}}},{and}} & (90) \\ {{{{Far}\text{-}{out}\mspace{14mu}\left( {\rho\operatorname{>>}{\lambda/8}} \right)\text{:}\mspace{14mu}{J_{\rho}(\rho)}} \sim J_{2}} = {\frac{j\;\gamma\;\omega\; Q_{1}}{4} \times \sqrt{\frac{2\;\lambda}{\pi}} \times {\frac{e^{{- {({\alpha + {j\;\beta}})}}\rho}}{\sqrt{\rho}}.}}} & (91) \end{matrix}$ where I₁ is the conduction current feeding the charge Q₁ on the first charge terminal T₁, and I₂ is the conduction current feeding the charge Q₂ on the second charge terminal T₂. The charge Q₁ on the upper charge terminal T₁ is determined by Q₁=C₁V₁, where C₁ is the isolated capacitance of the charge terminal T₁. Note that there is a third component to J₁ set forth above given by (E_(ρ) ^(Q) ¹ )/Z_(ρ), which follows from the Leontovich boundary condition and is the radial current contribution in the lossy conducting medium 203 pumped by the quasi-static field of the elevated oscillating charge on the first charge terminal Q₁. The quantity Z_(ρ)=jωμ_(o)/γ_(e) is the radial impedance of the lossy conducting medium, where γ_(e)=(jωμt₁σ₁−ω²μ₁ε₁)^(1/2).

The asymptotes representing the radial current close-in and far-out as set forth by equations (90) and (91) are complex quantities. According to various embodiments, a physical surface current J(ρ), is synthesized to match as close as possible the current asymptotes in magnitude and phase. That is to say close-in, |J(ρ)| is to be tangent to |J₁|, and far-out |J(ρ)| is to be tangent to |J₂|. Also, according to the various embodiments, the phase of J(ρ) should transition from the phase of J₁ close-in to the phase of J₂ far-out.

In order to match the guided surface wave mode at the site of transmission to launch a guided surface wave, the phase of the surface current |J₂| far-out should differ from the phase of the surface current |J₁| close-in by the propagation phase corresponding to e^(−jβ(ρ) ² ^(-ρ) ¹ ⁾ plus a constant of approximately 45 degrees or 225 degrees. This is because there are two roots for √{square root over (γ)}, one near π/4 and one near 5π/4. The properly adjusted synthetic radial surface current is

$\begin{matrix} {{J_{\rho}\left( {\rho,\phi,0} \right)} = {\frac{I_{o}\gamma}{4}{{H_{1}^{(2)}\left( {{- j}\;\gamma\;\rho} \right)}.}}} & (92) \end{matrix}$ Note that this is consistent with equation (17). By Maxwell's equations, such a J(ρ) surface current automatically creates fields that conform to

$\begin{matrix} {{H_{\phi} = {\frac{{- \gamma}\; I_{o}}{4}e^{{- u_{2}}z}{H_{1}^{(2)}\left( {{- j}\;\gamma\;\rho} \right)}}},} & (93) \\ {{E_{\rho} = {\frac{{- \gamma}\; I_{o}}{4}\left( \frac{u_{2}}{j\;\omega\; ɛ_{o}} \right)e^{{- u_{2}}z}{H_{1}^{(2)}\left( {{- j}\;\gamma\;\rho} \right)}}},{and}} & (94) \\ {E_{z} = {\frac{{- \gamma}\; I_{o}}{4}\left( \frac{- \gamma}{\omega\; ɛ_{o}} \right)e^{{- u_{2}}z}{{H_{0}^{(2)}\left( {{- j}\;\gamma\;\rho} \right)}.}}} & (95) \end{matrix}$ Thus, the difference in phase between the surface current |J₂| far-out and the surface current |J₁| close-in for the guided surface wave mode that is to be matched is due to the characteristics of the Hankel functions in equations (93)-(95), which are consistent with equations (1)-(3). It is of significance to recognize that the fields expressed by equations (1)-(6) and (17) and equations (92)-(95) have the nature of a transmission line mode bound to a lossy interface, not radiation fields that are associated with groundwave propagation.

In order to obtain the appropriate voltage magnitudes and phases for a given design of a guided surface waveguide probe 200 e at a given location, an iterative approach may be used. Specifically, analysis may be performed of a given excitation and configuration of a guided surface waveguide probe 200 e taking into account the feed currents to the terminals T₁ and T₂, the charges on the charge terminals T₁ and T₂, and their images in the lossy conducting medium 203 in order to determine the radial surface current density generated. This process may be performed iteratively until an optimal configuration and excitation for a given guided surface waveguide probe 200 e is determined based on desired parameters. To aid in determining whether a given guided surface waveguide probe 200 e is operating at an optimal level, a guided field strength curve 103 (FIG. 1) may be generated using equations (1)-(12) based on values for the conductivity of Region 1 (σ₁) and the permittivity of Region 1 (ε₁) at the location of the guided surface waveguide probe 200 e. Such a guided field strength curve 103 can provide a benchmark for operation such that measured field strengths can be compared with the magnitudes indicated by the guided field strength curve 103 to determine if optimal transmission has been achieved.

In order to arrive at an optimized condition, various parameters associated with the guided surface waveguide probe 200 e may be adjusted. One parameter that may be varied to adjust the guided surface waveguide probe 200 e is the height of one or both of the charge terminals T₁ and/or T₂ relative to the surface of the lossy conducting medium 203. In addition, the distance or spacing between the charge terminals T₁ and T₂ may also be adjusted. In doing so, one may minimize or otherwise alter the mutual capacitance C_(M) or any bound capacitances between the charge terminals T₁ and T₂ and the lossy conducting medium 203 as can be appreciated. The size of the respective charge terminals T₁ and/or T₂ can also be adjusted. By changing the size of the charge terminals T₁ and/or T₂, one will alter the respective self-capacitances C₁ and/or C₂, and the mutual capacitance C_(M) as can be appreciated.

Still further, another parameter that can be adjusted is the feed network 209 associated with the guided surface waveguide probe 200 e. This may be accomplished by adjusting the size of the inductive and/or capacitive reactances that make up the feed network 209. For example, where such inductive reactances comprise coils, the number of turns on such coils may be adjusted. Ultimately, the adjustments to the feed network 209 can be made to alter the electrical length of the feed network 209, thereby affecting the voltage magnitudes and phases on the charge terminals T₁ and T₂.

Note that the iterations of transmission performed by making the various adjustments may be implemented by using computer models or by adjusting physical structures as can be appreciated. By making the above adjustments, one can create corresponding “close-in” surface current J₁ and “far-out” surface current J₂ that approximate the same currents J(ρ) of the guided surface wave mode specified in Equations (90) and (91) set forth above. In doing so, the resulting electromagnetic fields would be substantially or approximately mode-matched to a guided surface wave mode on the surface of the lossy conducting medium 203.

While not shown in the example of FIG. 16, operation of the guided surface waveguide probe 200 e may be controlled to adjust for variations in operational conditions associated with the guided surface waveguide probe 200. For example, a probe control system 230 shown in FIG. 12 can be used to control the feed network 209 and/or positioning and/or size of the charge terminals T₁ and/or T₂ to control the operation of the guided surface waveguide probe 200 e. Operational conditions can include, but are not limited to, variations in the characteristics of the lossy conducting medium 203 (e.g., conductivity σ and relative permittivity ε_(r)), variations in field strength and/or variations in loading of the guided surface waveguide probe 200 e.

Referring now to FIG. 17, shown is an example of the guided surface waveguide probe 200 e of FIG. 16, denoted herein as guided surface waveguide probe 200 f. The guided surface waveguide probe 200 f includes the charge terminals T₁ and T₂ that are positioned along a vertical axis z that is substantially normal to the plane presented by the lossy conducting medium 203 (e.g., the Earth). The second medium 206 is above the lossy conducting medium 203. The charge terminal T₁ has a self-capacitance C₁, and the charge terminal T₂ has a self-capacitance C₂. During operation, charges Q₁ and Q₂ are imposed on the charge terminals T₁ and T₂, respectively, depending on the voltages applied to the charge terminals T₁ and T₂ at any given instant. A mutual capacitance C_(M) may exist between the charge terminals T₁ and T₂ depending on the distance there between. In addition, bound capacitances may exist between the respective charge terminals T₁ and T₂ and the lossy conducting medium 203 depending on the heights of the respective charge terminals T₁ and T₂ with respect to the lossy conducting medium 203.

The guided surface waveguide probe 200 f includes a feed network 209 that comprises an inductive impedance comprising a coil L_(1a) having a pair of leads that are coupled to respective ones of the charge terminals T₁ and T₂. In one embodiment, the coil L_(1a) is specified to have an electrical length that is one-half (½) of the wavelength at the operating frequency of the guided surface waveguide probe 200 f.

While the electrical length of the coil L_(1a) is specified as approximately one-half (½) the wavelength at the operating frequency, it is understood that the coil L_(1a) may be specified with an electrical length at other values. According to one embodiment, the fact that the coil L_(1a) has an electrical length of approximately one-half the wavelength at the operating frequency provides for an advantage in that a maximum voltage differential is created on the charge terminals T₁ and T₂. Nonetheless, the length or diameter of the coil L_(1a) may be increased or decreased when adjusting the guided surface waveguide probe 200 f to obtain optimal excitation of a guided surface wave mode. Adjustment of the coil length may be provided by taps located at one or both ends of the coil. In other embodiments, it may be the case that the inductive impedance is specified to have an electrical length that is significantly less than or greater than ½ the wavelength at the operating frequency of the guided surface waveguide probe 200 f.

The excitation source 212 can be coupled to the feed network 209 by way of magnetic coupling. Specifically, the excitation source 212 is coupled to a coil L_(P) that is inductively coupled to the coil L_(1a). This may be done by link coupling, a tapped coil, a variable reactance, or other coupling approach as can be appreciated. To this end, the coil L_(P) acts as a primary, and the coil L_(1a) acts as a secondary as can be appreciated.

In order to adjust the guided surface waveguide probe 200 f for the transmission of a desired guided surface wave, the heights of the respective charge terminals T₁ and T₂ may be altered with respect to the lossy conducting medium 203 and with respect to each other. Also, the sizes of the charge terminals T₁ and T₂ may be altered. In addition, the size of the coil L_(1a) may be altered by adding or eliminating turns or by changing some other dimension of the coil L_(1a). The coil L_(1a) can also include one or more taps for adjusting the electrical length as shown in FIG. 17. The position of a tap connected to either charge terminal T₁ or T₂ can also be adjusted.

Referring next to FIGS. 18A, 18B, 18C and 19, shown are examples of generalized receive circuits for using the surface-guided waves in wireless power delivery systems. FIGS. 18A and 18B-18C include a linear probe 303 and a tuned resonator 306, respectively. FIG. 19 is a magnetic coil 309 according to various embodiments of the present disclosure. According to various embodiments, each one of the linear probe 303, the tuned resonator 306, and the magnetic coil 309 may be employed to receive power transmitted in the form of a guided surface wave on the surface of a lossy conducting medium 203 according to various embodiments. As mentioned above, in one embodiment the lossy conducting medium 203 comprises a terrestrial medium (or Earth).

With specific reference to FIG. 18A, the open-circuit terminal voltage at the output terminals 312 of the linear probe 303 depends upon the effective height of the linear probe 303. To this end, the terminal point voltage may be calculated as V _(T)=∫₀ ^(h) ^(e) E _(inc) ·dl,  (96) where E_(inc) is the strength of the incident electric field induced on the linear probe 303 in Volts per meter, dl is an element of integration along the direction of the linear probe 303, and h_(e) is the effective height of the linear probe 303. An electrical load 315 is coupled to the output terminals 312 through an impedance matching network 318.

When the linear probe 303 is subjected to a guided surface wave as described above, a voltage is developed across the output terminals 312 that may be applied to the electrical load 315 through a conjugate impedance matching network 318 as the case may be. In order to facilitate the flow of power to the electrical load 315, the electrical load 315 should be substantially impedance matched to the linear probe 303 as will be described below.

Referring to FIG. 18B, a ground current excited coil 306 a possessing a phase shift equal to the wave tilt of the guided surface wave includes a charge terminal T_(R) that is elevated (or suspended) above the lossy conducting medium 203. The charge terminal T_(R) has a self-capacitance C_(R). In addition, there may also be a bound capacitance (not shown) between the charge terminal T_(R) and the lossy conducting medium 203 depending on the height of the charge terminal T_(R) above the lossy conducting medium 203. The bound capacitance should preferably be minimized as much as is practicable, although this may not be entirely necessary in every instance.

The tuned resonator 306 a also includes a receiver network comprising a coil L_(R) having a phase shift Φ. One end of the coil L_(R) is coupled to the charge terminal T_(R), and the other end of the coil L_(R) is coupled to the lossy conducting medium 203. The receiver network can include a vertical supply line conductor that couples the coil L_(R) to the charge terminal T_(R). To this end, the coil L_(R) (which may also be referred to as tuned resonator L_(R)-C_(R)) comprises a series-adjusted resonator as the charge terminal C_(R) and the coil L_(R) are situated in series. The phase delay of the coil L_(R) can be adjusted by changing the size and/or height of the charge terminal T_(R), and/or adjusting the size of the coil L_(R) so that the phase Φ of the structure is made substantially equal to the angle of the wave tilt Ψ. The phase delay of the vertical supply line can also be adjusted by, e.g., changing length of the conductor.

For example, the reactance presented by the self-capacitance C_(R) is calculated as 1/jωC_(R). Note that the total capacitance of the structure 306 a may also include capacitance between the charge terminal T_(R) and the lossy conducting medium 203, where the total capacitance of the structure 306 a may be calculated from both the self-capacitance C_(R) and any bound capacitance as can be appreciated. According to one embodiment, the charge terminal T_(R) may be raised to a height so as to substantially reduce or eliminate any bound capacitance. The existence of a bound capacitance may be determined from capacitance measurements between the charge terminal T_(R) and the lossy conducting medium 203 as previously discussed.

The inductive reactance presented by a discrete-element coil L_(R) may be calculated as jωL, where L is the lumped-element inductance of the coil L_(R). If the coil L_(R) is a distributed element, its equivalent terminal-point inductive reactance may be determined by conventional approaches. To tune the structure 306 a, one would make adjustments so that the phase delay is equal to the wave tilt for the purpose of mode-matching to the surface waveguide at the frequency of operation. Under this condition, the receiving structure may be considered to be “mode-matched” with the surface waveguide. A transformer link around the structure and/or an impedance matching network 324 may be inserted between the probe and the electrical load 327 in order to couple power to the load. Inserting the impedance matching network 324 between the probe terminals 321 and the electrical load 327 can effect a conjugate-match condition for maximum power transfer to the electrical load 327.

When placed in the presence of surface currents at the operating frequencies power will be delivered from the surface guided wave to the electrical load 327. To this end, an electrical load 327 may be coupled to the structure 306 a by way of magnetic coupling, capacitive coupling, or conductive (direct tap) coupling. The elements of the coupling network may be lumped components or distributed elements as can be appreciated.

In the embodiment shown in FIG. 18B, magnetic coupling is employed where a coil L_(S) is positioned as a secondary relative to the coil L_(R) that acts as a transformer primary. The coil L_(S) may be link-coupled to the coil L_(R) by geometrically winding it around the same core structure and adjusting the coupled magnetic flux as can be appreciated. In addition, while the receiving structure 306 a comprises a series-tuned resonator, a parallel-tuned resonator or even a distributed-element resonator of the appropriate phase delay may also be used.

While a receiving structure immersed in an electromagnetic field may couple energy from the field, it can be appreciated that polarization-matched structures work best by maximizing the coupling, and conventional rules for probe-coupling to waveguide modes should be observed. For example, a TE₂₀ (transverse electric mode) waveguide probe may be optimal for extracting energy from a conventional waveguide excited in the TE₂₀ mode. Similarly, in these cases, a mode-matched and phase-matched receiving structure can be optimized for coupling power from a surface-guided wave. The guided surface wave excited by a guided surface waveguide probe 200 on the surface of the lossy conducting medium 203 can be considered a waveguide mode of an open waveguide. Excluding waveguide losses, the source energy can be completely recovered. Useful receiving structures may be E-field coupled, H-field coupled, or surface-current excited.

The receiving structure can be adjusted to increase or maximize coupling with the guided surface wave based upon the local characteristics of the lossy conducting medium 203 in the vicinity of the receiving structure. To accomplish this, the phase delay (Φ) of the receiving structure can be adjusted to match the angle (Ψ) of the wave tilt of the surface traveling wave at the receiving structure. If configured appropriately, the receiving structure may then be tuned for resonance with respect to the perfectly conducting image ground plane at complex depth z=−d/2.

For example, consider a receiving structure comprising the tuned resonator 306 a of FIG. 18B, including a coil L_(R) and a vertical supply line connected between the coil L_(R) and a charge terminal T_(R). With the charge terminal T_(R) positioned at a defined height above the lossy conducting medium 203, the total phase shift Φ of the coil L_(R) and vertical supply line can be matched with the angle (Ψ) of the wave tilt at the location of the tuned resonator 306 a. From Equation (22), it can be seen that the wave tilt asymptotically passes to

$\begin{matrix} {{W = {{{W}e^{j\;\Psi}} = {\frac{E_{\rho}}{E_{z}}\underset{\rho\rightarrow\infty}{\longrightarrow}\frac{1}{\sqrt{ɛ_{r} - {j\frac{\sigma_{1}}{\omega\; ɛ_{o}}}}}}}},} & (97) \end{matrix}$ where ε_(r) comprises the relative permittivity and σ₁ is the conductivity of the lossy conducting medium 203 at the location of the receiving structure, ε_(o) is the permittivity of free space, and ω=2πf, where f is the frequency of excitation. Thus, the wave tilt angle (Ψ) can be determined from Equation (97).

The total phase shift (Φ=θ_(c)+θ_(y)) of the tuned resonator 306 a includes both the phase delay (θ_(c)) through the coil L_(R) and the phase delay of the vertical supply line (θ_(y)). The spatial phase delay along the conductor length l_(w) of the vertical supply line can be given by θ_(y)=β_(w)l_(w), where β_(w) is the propagation phase constant for the vertical supply line conductor. The phase delay due to the coil (or helical delay line) is θ_(c)=β_(p)l_(C), with a physical length of l_(C) and a propagation factor of

$\begin{matrix} {{\beta_{p} = {\frac{2\;\pi}{\lambda_{p}} = \frac{2\;\pi}{V_{f}\lambda_{0}}}},} & (98) \end{matrix}$ where V_(f) is the velocity factor on the structure, λ₀ is the wavelength at the supplied frequency, and λ_(p) is the propagation wavelength resulting from the velocity factor V_(f). One or both of the phase delays (θ_(c)+θ_(y)) can be adjusted to match the phase shift Φ to the angle (Ψ) of the wave tilt. For example, a tap position may be adjusted on the coil L_(R) of FIG. 18B to adjust the coil phase delay (θ_(c)) to match the total phase shift to the wave tilt angle (Φ=Ψ). For example, a portion of the coil can be bypassed by the tap connection as illustrated in FIG. 18B. The vertical supply line conductor can also be connected to the coil L_(R) via a tap, whose position on the coil may be adjusted to match the total phase shift to the angle of the wave tilt.

Once the phase delay (Ψ) of the tuned resonator 306 a has been adjusted, the impedance of the charge terminal T_(R) can then be adjusted to tune to resonance with respect to the perfectly conducting image ground plane at complex depth z=−d/2. This can be accomplished by adjusting the capacitance of the charge terminal T₁ without changing the traveling wave phase delays of the coil L_(R) and vertical supply line. The adjustments are similar to those described with respect to FIGS. 9A and 9B.

The impedance seen “looking down” into the lossy conducting medium 203 to the complex image plane is given by: Z _(in) =R _(in) +jX _(in) =Z _(o) tan h(jβ _(o)(d/2)),  (99) where β_(o)=ω√{square root over (μ_(o)ε_(o))}. For vertically polarized sources over the Earth, the depth of the complex image plane can be given by: d/2≈1/√{square root over (jωμ ₁σ₁−ω²μ₁ε₁)},  (100) where μ₁ is the permeability of the lossy conducting medium 203 and ε₁=ε_(r)ε_(o).

At the base of the tuned resonator 306 a, the impedance seen “looking up” into the receiving structure is Z_(↑)=Z_(base) as illustrated in FIG. 9A. With a terminal impedance of:

$\begin{matrix} {{Z_{R} = \frac{1}{j\;\omega\; C_{R}}},} & (101) \end{matrix}$ where C_(R) is the self-capacitance of the charge terminal T_(R), the impedance seen “looking up” into the vertical supply line conductor of the tuned resonator 306 a is given by:

$\begin{matrix} {{Z_{2} = {{Z_{W}\frac{Z_{R} + {Z_{W}{\tanh\left( {j\mspace{11mu}\beta_{W}h_{W}} \right)}}}{Z_{W} + {Z_{R}{\tanh\left( {j\;\beta_{W}h_{W}} \right)}}}} = {Z_{W}\frac{Z_{R} + {Z_{W}{\tanh\left( {j\;\theta_{y}} \right)}}}{Z_{W} + {Z_{R}{\tanh\left( {j\;\theta_{y}} \right)}}}}}},} & (102) \end{matrix}$ and the impedance seen “looking up” into the coil L_(R) of the tuned resonator 306 a is given by:

$\begin{matrix} {Z_{base} = {{R_{base} + {j\; X_{base}}} = {{Z_{R}\frac{Z_{2} + {Z_{R}{\tanh\left( {j\;\beta_{p}H} \right)}}}{Z_{R} + {Z_{2}{\tanh\left( {j\;\beta_{p}H} \right)}}}} = {Z_{c}{\frac{Z_{2} + {Z_{R}{\tanh\left( {j\;\theta_{c}} \right)}}}{Z_{R} + {Z_{2}{\tanh\left( {j\;\theta_{c}} \right)}}}.}}}}} & (103) \end{matrix}$ By matching the reactive component (X_(in)) seen “looking down” into the lossy conducting medium 203 with the reactive component (X_(base)) seen “looking up” into the tuned resonator 306 a, the coupling into the guided surface waveguide mode may be maximized.

Referring next to FIG. 180, shown is an example of a tuned resonator 306 b that does not include a charge terminal T_(R) at the top of the receiving structure. In this embodiment, the tuned resonator 306 b does not include a vertical supply line coupled between the coil L_(R) and the charge terminal T_(R). Thus, the total phase shift (Φ) of the tuned resonator 306 b includes only the phase delay (θ_(c)) through the coil L_(R). As with the tuned resonator 306 a of FIG. 18B, the coil phase delay θ_(c) can be adjusted to match the angle (Ψ) of the wave tilt determined from Equation (97), which results in Φ=Ψ. While power extraction is possible with the receiving structure coupled into the surface waveguide mode, it is difficult to adjust the receiving structure to maximize coupling with the guided surface wave without the variable reactive load provided by the charge terminal T_(R).

Referring to FIG. 18D, shown is a flow chart 180 illustrating an example of adjusting a receiving structure to substantially mode-match to a guided surface waveguide mode on the surface of the lossy conducting medium 203. Beginning with 181, if the receiving structure includes a charge terminal T_(R) (e.g., of the tuned resonator 306 a of FIG. 18B), then the charge terminal T_(R) is positioned at a defined height above a lossy conducting medium 203 at 184. As the surface guided wave has been established by a guided surface waveguide probe 200, the physical height (h_(p)) of the charge terminal T_(R) may be below that of the effective height. The physical height may be selected to reduce or minimize the bound charge on the charge terminal T_(R) (e.g., four times the spherical diameter of the charge terminal). If the receiving structure does not include a charge terminal T_(R) (e.g., of the tuned resonator 306 b of FIG. 18C), then the flow proceeds to 187.

At 187, the electrical phase delay Φ of the receiving structure is matched to the complex wave tilt angle Ψ defined by the local characteristics of the lossy conducting medium 203. The phase delay (θ_(c)) of the helical coil and/or the phase delay (θ_(y)) of the vertical supply line can be adjusted to make Φ equal to the angle (Ψ) of the wave tilt (W). The angle (Ψ) of the wave tilt can be determined from Equation (86). The electrical phase Φ can then be matched to the angle of the wave tilt. For example, the electrical phase delay Φ=θ_(c)+θ_(y) can be adjusted by varying the geometrical parameters of the coil L_(R) and/or the length (or height) of the vertical supply line conductor.

Next at 190, the load impedance of the charge terminal T_(R) can be tuned to resonate the equivalent image plane model of the tuned resonator 306 a. The depth (d/2) of the conducting image ground plane 139 (FIG. 9A) below the receiving structure can be determined using Equation (100) and the values of the lossy conducting medium 203 (e.g., the Earth) at the receiving structure, which can be locally measured. Using that complex depth, the phase shift (θ_(d)) between the image ground plane 139 and the physical boundary 136 (FIG. 9A) of the lossy conducting medium 203 can be determined using θ_(d)=β_(o) d/2. The impedance (Z_(in)) as seen “looking down” into the lossy conducting medium 203 can then be determined using Equation (99). This resonance relationship can be considered to maximize coupling with the guided surface waves.

Based upon the adjusted parameters of the coil L_(R) and the length of the vertical supply line conductor, the velocity factor, phase delay, and impedance of the coil L_(R) and vertical supply line can be determined. In addition, the self-capacitance (C_(R)) of the charge terminal T_(R) can be determined using, e.g., Equation (24). The propagation factor (β_(p)) of the coil L_(R) can be determined using Equation (98), and the propagation phase constant (β_(w)) for the vertical supply line can be determined using Equation (49). Using the self-capacitance and the determined values of the coil L_(R) and vertical supply line, the impedance (Z_(base)) of the tuned resonator 306 a as seen “looking up” into the coil L_(R) can be determined using Equations (101), (102), and (103).

The equivalent image plane model of FIG. 9A also applies to the tuned resonator 306 a of FIG. 18B. The tuned resonator 306 a can be tuned to resonance with respect to the complex image plane by adjusting the load impedance Z_(R) of the charge terminal T_(R) such that the reactance component X_(base) Of Z_(base) cancels out the reactance component of X_(in) of Z_(in), or X_(base)+X_(in)=0. Thus, the impedance at the physical boundary 136 (FIG. 9A) “looking up” into the coil of the tuned resonator 306 a is the conjugate of the impedance at the physical boundary 136 “looking down” into the lossy conducting medium 203. The load impedance Z_(R) can be adjusted by varying the capacitance (C_(R)) of the charge terminal T_(R) without changing the electrical phase delay Φ=θ_(c)+θ_(y) seen by the charge terminal T_(R). An iterative approach may be taken to tune the load impedance Z_(R) for resonance of the equivalent image plane model with respect to the conducting image ground plane 139. In this way, the coupling of the electric field to a guided surface waveguide mode along the surface of the lossy conducting medium 203 (e.g., Earth) can be improved and/or maximized.

Referring to FIG. 19, the magnetic coil 309 comprises a receive circuit that is coupled through an impedance matching network 333 to an electrical load 336. In order to facilitate reception and/or extraction of electrical power from a guided surface wave, the magnetic coil 309 may be positioned so that the magnetic flux of the guided surface wave, H_(φ), passes through the magnetic coil 309, thereby inducing a current in the magnetic coil 309 and producing a terminal point voltage at its output terminals 330. The magnetic flux of the guided surface wave coupled to a single turn coil is expressed by

=∫∫_(A) _(CS) μ_(r)μ_(o)

·{circumflex over (n)}dA  (104) where

is the coupled magnetic flux, μ_(r) is the effective relative permeability of the core of the magnetic coil 309, μ_(o) is the permeability of free space,

is the incident magnetic field strength vector, {circumflex over (n)} is a unit vector normal to the cross-sectional area of the turns, and A_(CS) is the area enclosed by each loop. For an N-turn magnetic coil 309 oriented for maximum coupling to an incident magnetic field that is uniform over the cross-sectional area of the magnetic coil 309, the open-circuit induced voltage appearing at the output terminals 330 of the magnetic coil 309 is

$\begin{matrix} {{V = {{{- N}\frac{d\;\mathcal{F}}{d\; t}} \approx {{- j}\;\omega\;\mu_{r}\mu_{0}N\; H\; A_{CS}}}},} & (105) \end{matrix}$ where the variables are defined above. The magnetic coil 309 may be tuned to the guided surface wave frequency either as a distributed resonator or with an external capacitor across its output terminals 330, as the case may be, and then impedance-matched to an external electrical load 336 through a conjugate impedance matching network 333.

Assuming that the resulting circuit presented by the magnetic coil 309 and the electrical load 336 are properly adjusted and conjugate impedance matched, via impedance matching network 333, then the current induced in the magnetic coil 309 may be employed to optimally power the electrical load 336. The receive circuit presented by the magnetic coil 309 provides an advantage in that it does not have to be physically connected to the ground.

With reference to FIGS. 18A, 18B, 18C and 19, the receive circuits presented by the linear probe 303, the mode-matched structure 306, and the magnetic coil 309 each facilitate receiving electrical power transmitted from any one of the embodiments of guided surface waveguide probes 200 described above. To this end, the energy received may be used to supply power to an electrical load 315/327/336 via a conjugate matching network as can be appreciated. This contrasts with the signals that may be received in a receiver that were transmitted in the form of a radiated electromagnetic field. Such signals have very low available power, and receivers of such signals do not load the transmitters.

It is also characteristic of the present guided surface waves generated using the guided surface waveguide probes 200 described above that the receive circuits presented by the linear probe 303, the mode-matched structure 306, and the magnetic coil 309 will load the excitation source 212 (e.g., FIGS. 3, 12 and 16) that is applied to the guided surface waveguide probe 200, thereby generating the guided surface wave to which such receive circuits are subjected. This reflects the fact that the guided surface wave generated by a given guided surface waveguide probe 200 described above comprises a transmission line mode. By way of contrast, a power source that drives a radiating antenna that generates a radiated electromagnetic wave is not loaded by the receivers, regardless of the number of receivers employed.

Thus, together one or more guided surface waveguide probes 200 and one or more receive circuits in the form of the linear probe 303, the tuned mode-matched structure 306, and/or the magnetic coil 309 can make up a wireless distribution system. Given that the distance of transmission of a guided surface wave using a guided surface waveguide probe 200 as set forth above depends upon the frequency, it is possible that wireless power distribution can be achieved across wide areas and even globally.

The conventional wireless-power transmission/distribution systems extensively investigated today include “energy harvesting” from radiation fields and also sensor coupling to inductive or reactive near-fields. In contrast, the present wireless-power system does not waste power in the form of radiation which, if not intercepted, is lost forever. Nor is the presently disclosed wireless-power system limited to extremely short ranges as with conventional mutual-reactance coupled near-field systems. The wireless-power system disclosed herein probe-couples to the novel surface-guided transmission line mode, which is equivalent to delivering power to a load by a waveguide or a load directly wired to the distant power generator. Not counting the power required to maintain transmission field strength plus that dissipated in the surface waveguide, which at extremely low frequencies is insignificant relative to the transmission losses in conventional high-tension power lines at 60 Hz, all of the generator power goes only to the desired electrical load. When the electrical load demand is terminated, the source power generation is relatively idle.

Referring next to FIGS. 20A-E, shown are examples of various schematic symbols that are used with reference to the discussion that follows. With specific reference to FIG. 20A, shown is a symbol that represents any one of the guided surface waveguide probes 200 a, 200 b, 200 c, 200 e, 200 d, or 200 f, or any variations thereof. In the following drawings and discussion, a depiction of this symbol will be referred to as a guided surface waveguide probe P. For the sake of simplicity in the following discussion, any reference to the guided surface waveguide probe P is a reference to any one of the guided surface waveguide probes 200 a, 200 b, 200 c, 200 e, 200 d, or 200 f, or variations thereof.

Similarly, with reference to FIG. 20B, shown is a symbol that represents a guided surface wave receive structure that may comprise any one of the linear probe 303 (FIG. 18A), the tuned resonator 306 (FIGS. 18B-18C), or the magnetic coil 309 (FIG. 19). In the following drawings and discussion, a depiction of this symbol will be referred to as a guided surface wave receive structure R. For the sake of simplicity in the following discussion, any reference to the guided surface wave receive structure R is a reference to any one of the linear probe 303, the tuned resonator 306, or the magnetic coil 309 or variations thereof.

Further, with reference to FIG. 20C, shown is a symbol that specifically represents the linear probe 303 (FIG. 18A). In the following drawings and discussion, a depiction of this symbol will be referred to as a guided surface wave receive structure R_(P). For the sake of simplicity in the following discussion, any reference to the guided surface wave receive structure R_(P) is a reference to the linear probe 303 or variations thereof.

Further, with reference to FIG. 20D, shown is a symbol that specifically represents the tuned resonator 306 (FIGS. 18B-18C). In the following drawings and discussion, a depiction of this symbol will be referred to as a guided surface wave receive structure R_(R). For the sake of simplicity in the following discussion, any reference to the guided surface wave receive structure R_(R) is a reference to the tuned resonator 306 or variations thereof.

Further, with reference to FIG. 20E, shown is a symbol that specifically represents the magnetic coil 309 (FIG. 19). In the following drawings and discussion, a depiction of this symbol will be referred to as a guided surface wave receive structure R_(M). For the sake of simplicity in the following discussion, any reference to the guided surface wave receive structure R_(M) is a reference to the magnetic coil 309 or variations thereof.

With reference to FIG. 21, shown is an example of a modulated transmission system such as an Amplitude Modulation (AM) transmission system 400 according to one embodiment of the present disclosure. The AM transmission system 400 includes an AM transmitter 403, a matching network 406, a guided surface waveguide probe P, and potentially other components.

In the following discussion, the various embodiments are discussed with reference to Amplitude Modulation (AM). However, it is understood that many other types of modulation may be employed. Consequently, as described herein, an AM transmitter provides an example of the various types of transmitters that may be employed. To this end, other types of modulation that may be employed beyond AM transmission may comprise, for example, frequency modulation, frequency-shift keying, packet modulation, and other modulation techniques. Accordingly, where reference is made to an AM transmitter or another other component or aspect involved in AM transmission, it is understood that the same principles apply to other modulation techniques and that such other modulation equipment and techniques may be substituted for AM transmission where appropriate. Thus, as contemplated herein, terms such as a modulation transmitter, modulated signal, and the like refer to all types of modulation and not merely amplitude modulation. Accordingly, as described herein, an amplitude modulation transmission system is merely an example of a modulated transmission system, an AM transmitter is merely an example of a modulation transmitter or an AM signal is merely an example of a modulated signal.

As shown in FIG. 21, the AM transmitter 403 includes an AM subsystem 409, a carrier source 413, an information signal source 416, and an amplifier 419. In addition, the AM transmitter 403 may comprise other elements as well. According to one embodiment, the AM transmitter 403 is one example of amplitude modulation circuitry that is employed to generate an AM signal as will described. The AM subsystem 409 receives both an information signal 423 from the information signal source 416 and a carrier signal 426 from the carrier source 413. The carrier source 413 may comprise, for example, and oscillator or other source that generates the carrier signal 426 at a desired transmission frequency.

The information signal 423 is used to modulate the carrier signal 426. The information signal source 416 that generates the information signal 423 may be, for example, a microphone, audio reproduction equipment, or other source as can be appreciated. The information signal source 416 may include various components to provide for signal processing or conditioning such as noise reduction, equalization, pre-amplification, or other signal processing as can be appreciated. The information signal 423 may also be called a “modulation signal” since it is used to modulate the carrier signal 426.

The AM subsystem 409 generates an AM signal 429 from the information signal 423 and the carrier signal 426. To this end, the AM subsystem 409 may implement any one of a number of different types of amplitude modulation. Such types of amplitude modulation may comprise, for example, double-sideband full carrier, single-sideband reduced-carrier, single-sideband full-carrier, single-sideband suppressed-carrier, independent-sideband emission, vestigial-sideband, linked compressor and expander, or other types of amplitude modulation.

The AM subsystem 409 may be an analog or digital circuit. For example, the AM subsystem 409 may employ digital signal processing to generate the AM signal 429. To this end, analog-to-digital conversion may be performed on the information signal 423 and the carrier signal 426 within the modulation subsystem 409 unless such signals are already in digital form before being applied to the modulation subsystem 409. Alternatively, the modulation subsystem 409 may comprise analog components where the carrier signal 426 and the information signal 423 are analog signals.

The AM signal 429 may be applied to an amplifier 419 where it is amplified, thereby generating an output AM signal 433. Alternatively, some other components might be used instead of the amplifier 419 to generate a desired output AM signal 433. The output AM signal 433 is then sent to the guided surface waveguide probe P through the matching network 406. To this end, the matching network 406 may comprise one or more circuit elements configured to facilitate coupling the output AM signal 433 to the guided surface waveguide probe P while minimizing reflection as can be appreciated. According to one embodiment, the AM transmitter 403/matching network 406 may be coupled directly to the guided surface waveguide probe P by way of a direct coupling. Alternatively, the AM transmitter 403/matching network 406 may be inductively coupled or link-coupled to the guided surface waveguide probe P as will be described. It should be noted that the matching network 406 is employed to minimize or eliminate unwanted reflection in the system. To this end, when the AM transmitter 403 is coupled to any embodiment of a guided surface waveguide probe as described herein, various approaches used for impedance matching should be considered to eliminate unwanted reflection.

Next, the general operation of the AM transmission system 400 is described. To begin, the carrier source 413 generates the carrier signal 426, and the information signal source 416 generates the information signal 423. The information signal 423 and the carrier signal 426 are both applied to the modulation subsystem 409. The modulation subsystem 409 generates the AM signal 429 that is amplified by the amplifier 419, thereby generating the output AM signal 433. The output AM signal 433 is then applied to the guided surface waveguide probe P through the matching network 406. In some cases, the matching network 406 may not be necessary as will be described. Also, it may be understood that the matching network 406 may be incorporated as part of the AM transmitter 403.

The guided surface waveguide probe P is adjusted to launch a guided surface wave that embodies the amplitude modulated signal along the surface of the ground which is also termed a “terrestrial medium” as described above. The guided surface wave propagates along the interface between the terrestrial medium and the atmospheric medium as described above. To launch the guided surface wave, the guided surface waveguide probe P is adjusted to generate a resultant field that provides for the complex angle of incidence at least at a Hankel crossover distance from the guided surface waveguide probe P as described above. The complex angle of incidence may be calculated as described above.

According to the various embodiments, the guided surface wave that embodies the amplitude modulated signal decays exponentially as a function of distance from the guided surface waveguide probe P. In this respect, the guided surface wave that embodies the amplitude modulated signal is a transmission line mode. Consequently, receivers such as an AM radio will present an electrical load to the AM transmitter 403 coupled to the guided surface waveguide probe P. However, given that the typical AM radio is locally powered, the electrical load that such a receiver will present to the AM transmitter 403 is very small if not negligible.

In fact, it is believed that the electrical load presented by a given AM radio would be measured in terms of Picowatts. Given this reality, it would not be possible to come up with enough receivers to present much of a change in the electrical load experienced by the AM transmitter 403 by AM radios. Thus, ultimately, the electrical load seen by AM transmitter 403 and the guided surface waveguide probe P is likely to be relatively constant and primarily involves resistive losses in the ground, guided surface waveguide probe P, the AM transmitter 403, and any other component in the overall system.

Over time, the ground may be subject to change due to changing weather conditions and the like. For example, dry ground due to sun exposure might become wet due to a passing storm. As such, the conductivity and permittivity of the ground will change. Given that the electrical load experienced by the guided surface waveguide probe P is not likely to fluctuate significantly, according to various embodiments, the guided surface waveguide probe P may include control systems to adjust the operation of the guided surface waveguide probe P itself for optimal transmission as will be described.

Alternatively, in some embodiments, the guided surface waveguide probe P may be static in nature without control systems to adjust the operation of the guided surface waveguide probe P itself for optimal transmission relative to changing conditions on the ground, etc. In such an embodiment, it may be the case that efficiency in transmitting a guided surface wave may be affected by changing conductivity and permittivity of the ground. However, in some environments the changes to the conductivity and permittivity of the ground may not be that significant from one weather extreme (rain or snow) to another (dry conditions) to affect the operation of the guided surface waveguide probe P significantly. To the extent that any inefficiencies that are introduced by changing weather conditions, such inefficiencies may be tolerated where a static guided surface waveguide probe P is employed.

According to one embodiment, the amplifier 419 or other appropriate component of the AM transmitter 403 is controlled to drive the output AM signal 433 in a manner so as to maintain a constant voltage on an upper charge terminal T₁ (FIG. 7) of the guided surface waveguide probe P. Since the strength of the resulting electromagnetic field embodied in the guided surface wave launched by the guided surface waveguide probe P is proportional to the voltage on the charge terminal T₁, the voltage level maintained will depend upon the ultimate desired strength of the electromagnetic field of the guided surface wave. Note that where the conductivity and permittivity of the ground changes, the efficiency of the guided surface waveguide probe P in launching the guided surface wave may increase or decrease accordingly. As such, the a control system may be configured to maintain optimum launching efficiency with respect to launching the guided surface wave so that energy is not lost by driving the output AM signal 433 unnecessarily with more power via the amplifier 419. In other words, if the launching efficiency of the guided surface waveguide probe P is compromised and the amplifier 419 works harder to maintain the desired voltage and field strength, then it may be the case that energy is unnecessarily being wasted in the system.

To help maintain optimal operation, a feedback signal may be generated based on the magnitude of power produced by the amplifier 419 in driving the guided surface waveguide probe P, where the expected electrical load experienced by the guided surface waveguide probe P is to remain constant as is the case with the amplitude modulation transmission system 400 described herein. If the amount of power supplied to the guided surface waveguide probe P exceeds expected values, then the launching efficiency may not be optimum and adjustment of the operation of the guided surface waveguide probe P may be desirable. Specific adjustments that may be made with respect to the operation of the guided surface waveguide probe P are discussed with reference to later figures.

Due to the fact that the guided surface waveguide probe P launches a guided surface wave that is a transmission line mode, the electromagnetic field of the guided surface wave decays exponentially as a function of distance from the guided surface waveguide probe P. In addition, the guided surface wave does not spread hemispherically, but is bound to the terrestrial medium and spreads as a function of e^(−αd)/√{square root over (d)} (where d=distance) and exhibits a distinctive knee on the log-log scale. The fact that the guided surface wave generated by a guided surface waveguide probe P decays exponentially and is not subject to hemispherical spreading means that the field strength before the knee of the curve is much greater than one would achieve with a comparable conventional quarter-wavelength antenna. The fact that the guided surface wave that embodies the amplitude modulated signal has such a shape means that the electromagnetic fields generated by the guided surface waveguide probe P are much stronger than radiated fields generated by a conventional quarter-wavelength antenna. At some distances, the field strength of the guided surface wave may be 100 to 1000 times stronger (or more) than such radiated fields.

In addition, one may recall that in order to generate a radiated field using a conventional antenna, radiation resistance is maximized. The electrical length of such an antenna is specified so as to maximize radiation resistance. One convention is to use an antenna that is at least a quarter-wavelength in height.

However, according to various embodiments, the electrical length of the guided surface waveguide probe P is electrically small so as to minimize radiation resistance, which in turn minimizes or substantially eliminates the generation of radiated electromagnetic waves by the structure. According to one embodiment, the electrical length of the guided surface waveguide probe P is less than 1/10^(th) the height of a conventional quarter-wavelength antenna operating at the same frequency, although other electrical lengths may be employed. Assuming that a guided surface waveguide probe P is configured to minimize radiation resistance, then such a structure provides a significant advantage in that the guided surface waveguide probe P may be much smaller in size than a traditional antenna. This translates into a smaller area required to mount the guided surface waveguide probe P when considering the need for guy wires and the like to hold a larger antenna structure in place.

In one further embodiment, it would be possible for the electrical height of the guided surface waveguide probe P to be specified so that the amplitude modulated signal 429 is embodied in both a guided surface wave launched and a radiated field transmitted by the a modified version of a guided surface waveguide probe P.

With reference to FIG. 22, shown is another example of a modulated transmission system comprising an Amplitude Modulation (AM) transmission system 400 a according to one embodiment of the present disclosure. The AM transmission system 400 a is a specific example of the AM transmission system 400 (FIG. 21) described above. The AM transmission system 400 a includes the AM transmitter 403, the matching network 406, and a guided surface waveguide probe P₁ that is similar to the guided surface waveguide probe 200 b (FIG. 7). The AM transmitter 403 is the same as was described with reference to FIG. 21 and includes the carrier source 413, the information signal source 416, the AM subsystem 409, the amplifier 419, and potentially other components as described above. Accordingly, a detailed discussion of the operation of the AM transmitter 403 is not provided with reference to FIG. 22 as the same is set forth in the discussion of FIG. 21 above.

The AM transmitter 403 is coupled to a matching network 406, which in turn, is directly coupled to the guided surface waveguide probe P₁. Alternatively, the matching network 406 may be inductively coupled or link-coupled to the guided surface waveguide probe P₁.

According to one embodiment, guided surface waveguide probe P₁ is a single phase probe having a single charge terminal T₁. The guided surface waveguide probe P₁ includes a coil 453. One end of the coil 453 is coupled to the charge terminal T₁, and the other end of the coil 453 is coupled to a ground stake 456 or other grounding mechanism. The coil 453 provides one example of a phase delay circuit that may be used in the feed network of the guided surface waveguide probe P₁. It is understood that other phase delay circuits may be employed as mentioned above.

Next, the general operation of the AM transmission system 400 a is described. To begin, the AM transmitter 403 generates an output AM signal 433 that is applied to the guided surface waveguide probe P₁ through the matching network 406. As mentioned above, in some situations the matching network 406 may not be necessary where the output impedance of the AM transmitter 403 is impedance matched to the guided surface waveguide probe P₁. Specifically, if the output impedance of the AM transmitter 403 is known, the output of the AM transmitter 403 may be coupled to tap at an appropriate location on the coil 453 to match the output impedance of the AM transmitter 403 to eliminate unwanted reflections.

The guided surface waveguide probe P₁ is adjusted to launch a guided surface wave that embodies the AM signal along the surface of the ground or terrestrial medium as described above. To this end, the guided surface wave propagates along the interface between the terrestrial medium and the atmospheric medium as described above. The guided surface waveguide probe P₁ is adjusted to generate a resultant field that provides for the complex angle of incidence at least at a Hankel crossover distance from the guided surface waveguide probe P₁ as described above. Stated further, the charge terminal T₁ elevated over the terrestrial medium or the lossy conducting medium is configured to generate at least one resultant field that synthesizes a wave front incident at the complex Brewster angle of incidence (θ_(i,B)) of the terrestrial medium or the lossy conducting medium. The complex angle of incidence or complex Brewster angle of incidence may be calculated as described above.

The coil 453 and feed lines between the coil 453 (and the switching mechanism 364) and the charge terminal T₁ comprise a feed network that is electrically coupled to the charge terminal T₁. This feed network provides for a phase delay (Φ) that matches a wave tilt angle (Ψ) associated with a complex Brewster angle of incidence (θ_(i,B)) associated with the terrestrial medium (which is a lossy conducting medium) in the vicinity of the guided surface waveguide probe P₁.

As was discussed above, the guided surface wave that embodies the amplitude modulated signal decays exponentially as a function of distance from the guided surface waveguide probe P₁. In this respect, the guided surface wave that embodies the amplitude modulated signal is a transmission line mode. Consequently, receivers such as an AM radio will present an electrical load to the AM transmitter 403 and the guided surface waveguide probe P₁. However, given that the typical AM radio is locally powered, the electrical load that such a receiver will present to the guided surface waveguide probe P₁ is very small if not negligible as mentioned above. Ultimately, the electrical load seen by the guided surface waveguide probe P₁ is likely to be very small and relatively constant as was described above with respect to the guided surface waveguide probe P (FIG. 21).

As was mentioned above, over time the ground or terrestrial medium may be subject to change due to changing weather conditions and the like. For example, dry ground due to sun exposure might become wet due to a passing storm. As such, the conductivity and permittivity of the ground will change. It is possible that the efficiency of the operation of the guided surface waveguide probe P₁ may be effected by the changing conductivity and permittivity in such cases. However, in some situations, the effect of changing conductivity and permittivity on the operation of the guided surface waveguide probe P₁ may be within an acceptable or tolerable limits. As such, the AM transmitter 403 may compensate for any efficiency by providing more power to the system. To this end a feedback signal may be generated from an ammeter at the base of the guided surface waveguide probe P₁ of from a field meter near the site of transmission that is provided to the AM transmitter 403 so that the AM transmitter 403 can work to maintain a constant voltage on the terminal T₁ despite changing conditions around the site of transmission. In any event, according to one embodiment, amplifier 419 or other appropriate component of the AM transmitter 403 is controlled to drive the output AM signal 433 in a manner so as to maintain a constant voltage on the charge terminal T₁.

With reference to FIG. 23, shown is yet another example of a modulated transmission system comprising an Amplitude Modulation (AM) transmission system 400 b according to one embodiment of the present disclosure. The AM transmission system 400 b is another specific example of the AM transmission system 400 (FIG. 21) described above. The AM transmission system 400 b includes the AM transmitter 403, the matching network 406, and a guided surface waveguide probe P₂ that is similar to the guided surface waveguide probe 200 b (FIG. 7) with some differences as will be described below. The AM transmitter 403 is the same as was described with reference to FIG. 21 and includes the carrier source 413, the information signal source 416, the AM subsystem 409, the amplifier 419, and potentially other components as described above. Accordingly, a detailed discussion of the operation of the AM transmitter 403 is not provided with reference to FIG. 23 as the same is set forth in the discussion of FIG. 21 above.

The AM transmitter 403 is coupled to a matching network 406, which in turn, is directly coupled to the guided surface waveguide probe P₂. Alternatively, the matching network 406 may be inductively coupled or link-coupled to the guided surface waveguide probe P₂.

According to one embodiment, guided surface waveguide probe P₂ is a single phase probe having a single charge terminal T₁ similar to the guided surface waveguide probe P₁ (FIG. 22). To this end, the guided surface waveguide probe P₂ includes the coil 453. One end of the coil 453 is coupled to the charge terminal T₁, and the other end of the coil 453 is coupled to the ground stake 456 or other grounding mechanism. An ammeter 459 is positioned at the ground stake 456 to measure the current at that point. The coil 453 provides one example of a phase delay circuit that may be used in the feed network of the guided surface waveguide probe P₂. It is understood that other phase delay circuits may be employed as mentioned above.

The guided surface waveguide probe P₂ further includes a switching mechanism 463. The switching mechanism 463 may comprise, for example, roller in a roller inductor, a solid state device such as a multiplexer, a mechanical switching device, or other configuration. Where the switching mechanism is a roller in a roller inductor, the coil 453 is part of the roller inductor as will be described in further detail below. The specific type of switching mechanism 463 used will depend upon the voltage and current handling requirements for a given guided surface waveguide probe P (FIG. 21). An input of the switching mechanism 463 is coupled to the charge terminal T₁. The switching mechanism 463 has a plurality of outputs coupled to taps on the coil 453. At any given time, depending on its state, the switching mechanism 463 couples the charge terminal T₁ to a respective one of the taps, thereby coupling the charge terminal T₁ to a respective point on the coil 453. In this manner, the phase delay due to the coil 453 may be adjusted to provide for optimal operation of the guided surface waveguide probe P₂ depending on the physical parameters of the ground that may change from time to time due to weather or other factors.

To this end, the guided surface waveguide probe P₂ also includes a waveguide probe control system 466. The waveguide probe control system 466 controls the position of the switching mechanism 463 to optimize the operation of the guided surface waveguide probe P₂ as will be described. A control output from the waveguide probe control system 466 is coupled to a control input of the switching mechanism 463 and allows the waveguide probe control system 466 to direct the state of the switching mechanism 463 to determine the tap to which the charge terminal T₁ is connected at any given time.

It should be noted that a field meter 469 may also be coupled to the waveguide probe control system 466 to provide field strength readings thereto. According to various embodiments, the field meter 469 may be employed in place of the ammeter 459 or in addition to the ammeter 459.

Next, the general operation of the AM transmission system 400 b is described. To begin, the AM transmitter 403 generates an output AM signal 433 that is applied to the guided surface waveguide probe P₂ through the matching network 406. As mentioned above, the matching network 406 may not be necessary.

The guided surface waveguide probe P₂ is adjusted to launch a guided surface wave that embodies the AM signal along the surface of the ground or terrestrial medium as described above. To this end, the guided surface wave propagates along the interface between the terrestrial medium and the atmospheric medium as described above. The guided surface waveguide probe P₂ is adjusted to generate a resultant field that provides for the complex angle of incidence at least at a Hankel crossover distance from the guided surface waveguide probe P₂ as described above. Stated further, the charge terminal T₁ elevated over the terrestrial medium or the lossy conducting medium is configured to generate at least one resultant field that synthesizes a wave front incident at the complex Brewster angle of incidence (θ_(i,B)) of the terrestrial medium or the lossy conducting medium. The complex angle of incidence or complex Brewster angle of incidence may be calculated as described above.

Alternatively, the coil 453 and feed lines between the coil 453 (and the switching mechanism 364) and the charge terminal T₁ comprise a feed network that is electrically coupled to the charge terminal T₁. This feed network provides for a phase delay (Φ) that matches a wave tilt angle (Ψ) associated with a complex Brewster angle of incidence (θ_(i,B)) associated with the terrestrial medium (which is a lossy conducting medium) in the vicinity of the guided surface waveguide probe P₂.

As was discussed above, the guided surface wave that embodies the amplitude modulated signal decays exponentially as a function of distance from the guided surface waveguide probe P₂. In this respect, the guided surface wave that embodies the amplitude modulated signal is a transmission line mode. Consequently, receivers such as an AM radio will present an electrical load to the AM transmitter 403 and the guided surface waveguide probe P₂. However, given that the typical AM radio is locally powered, the electrical load that such a receiver will present to the guided surface waveguide probe P₂ is very small if not negligible as mentioned above. Ultimately, the electrical load seen by the guided surface waveguide probe P₂ is likely to be very small and relatively constant as was described above with respect to the guided surface waveguide probe P (FIG. 21).

As was mentioned above, over time the ground or terrestrial medium may be subject to change due to changing weather conditions and the like. For example, dry ground due to sun exposure might become wet due to a passing storm. As such, the conductivity and permittivity of the ground will change. Given that the electrical load experienced by the guided surface waveguide probe P₂ is not likely to fluctuate significantly, the waveguide probe control system 466 can be configured to adjust the taps by controlling the switching mechanism 463 using the current at the ground stake 456 as detected by the ammeter 459, or the field strength as detected by the field meter 469, as feedback in order to optimize the launching of the guided surface wave.

Ultimately, the taps may be adjusted to optimize the operation of the guided surface waveguide probe P₂. According to one embodiment, the operation of the guided surface waveguide probe P₂ is optimized when the current at the ground stake 456 is maximized or when the field strength of the guided surface wave generated by the guided surface waveguide probe is maximized. Thus, in one embodiment, the taps may be adjusted in order to maximize current at the ground stake 456 as detected by the ammeter 459 or to maximize the field strength measured by the field meter 469 to ensure optimal operation in view of changing ground conditions or other conditions. As an alternative, the waveguide probe control system 466 may obtain a feedback signal from a ground parameter meter that provides current values of conductivity and permittivity for the ground local to the guided surface waveguide probe P₂ as described above. The guided surface waveguide probe P₂ may be adjusted to substantially match an optimal configuration of the guided surface waveguide probe P₂ as calculated from the values of conductivity and permittivity of the ground at the site of the guided surface waveguide probe P₂.

According to one embodiment, amplifier 419 or other appropriate component of the AM transmitter 403 is controlled to drive the output AM signal 433 in a manner so as to maintain a constant voltage on the charge terminal T₁. Since the strength of the resulting electromagnetic field embodied in the guided surface wave launched by the guided surface waveguide probe P₂ is proportional to the voltage on the charge terminal T₁, the voltage level maintained will depend upon the ultimate desired strength of the electromagnetic field of the guided surface wave. Note that where the conductivity and permittivity of the ground changes, the efficiency of the guided surface waveguide probe P₂ in launching the guided surface wave may increase or decrease accordingly. As such, the waveguide probe control system 466 is configured to maintain optimum launching efficiency with respect to launching the guided surface wave so that energy is not lost by driving the output AM signal 433 with more energy that is necessary via the amplifier 419. In other words, if the launching efficiency of the guided surface waveguide probe P₂ is compromised and the AM transmitter 403 is forced to harder (via the amplifier) to maintain the desired voltage and field strength, then it may be the case that energy is unnecessarily being wasted in the system. To this end, it is also possible that a feedback signal may be generated based on the magnitude of power output produced by the AM transmitter 403 in driving the guided surface waveguide probe P₂, where the expected electrical load experienced by the guided surface waveguide probe P₂ is to remain constant as is the case with the amplitude modulation transmission system 400 described herein. If the amount of power supplied to the guided surface waveguide probe P₂ exceeds expected values, then the launching efficiency may not be optimum and adjustment of the taps via the switching mechanism 463 may be desirable. Alternatively, other parameters of the guided surface waveguide probe P₂ might be adjusted. Note that a signal may be sent from the AM transmitter 403 to the waveguide probe control system 466 to provide an indication as to whether energy is being wasted due to the fact that the AM transmitter 403 is overdriving the guided surface waveguide probe P₂.

With reference to FIG. 24, shown is yet another example of a modulated transmission system comprising an Amplitude Modulation (AM) transmission system 400 c according to one embodiment of the present disclosure. The AM transmission system 400 c is another example of the AM transmission system 400 (FIG. 21) described above. The AM transmission system 400 c includes the AM transmitter 403, the matching network 406, and a guided surface waveguide probe P₃ that is similar to the guided surface waveguide probe 200 d (FIG. 14). The AM transmitter 403 is the same as was described with reference to FIG. 21 and includes the carrier source 413, the information signal source 416, the AM subsystem 409, the amplifier 419, and potentially other components as described above. Accordingly, a detailed discussion of the operation of the AM transmitter 403 is not provided with reference to FIG. 24 as the same is set forth in the discussion of FIG. 21 above.

According to one embodiment, guided surface waveguide probe P₃ is a single phase probe having a single charge terminal T₁ with a compensation terminal 473. The guided surface waveguide probe P₃ includes the coil 453. One end of the coil 453 is coupled to the charge terminal T₁, and the other end of the coil 453 is coupled to the ground stake 456 or other grounding mechanism. An ammeter 459 is positioned at the ground stake 456 to measure the current at that point. The coil 453 provides one example of a phase delay circuit that may be used in the feed network of the guided surface waveguide probe P₃. It is understood that other phase delay circuits may be employed as mentioned above.

The guided surface waveguide probe P₃ further includes a switching mechanism 476 that is similar to the switching mechanism 463 discussed above with reference to FIG. 23. However, the guided surface waveguide probe P₃ differs from the guided surface waveguide probe P₂ (FIG. 23) in that an input of the switching mechanism 463 is coupled to the compensation terminal 473. The switching mechanism 2049 has a plurality of outputs coupled to taps on the coil 453. At any given time, depending on its state, the switching mechanism 463 couples the compensation terminal 473 to a respective one of the taps.

The guided surface waveguide probe P₃ also includes a waveguide probe control system 479. The waveguide probe control system 479 controls the position of the switching mechanism 463 to optimize the operation of the guided surface waveguide probe P₃ in a similar manner to the waveguide probe control system 466 (FIG. 23) described above. To this end, a control output from the waveguide probe control system 479 is coupled to a control input of the switching mechanism 476 and allows the waveguide probe control system 479 to direct the state of the switching mechanism 476 to determine the tap to which the compensation terminal 473 is connected at any given time.

The guided surface waveguide probe P₃ is adjusted to launch a guided surface wave that embodies the amplitude modulated signal along the surface of the ground or terrestrial medium as described above. To this end, the guided surface wave propagates along the interface between the terrestrial medium and the atmospheric medium as described above. The guided surface waveguide probe P₃ is adjusted to generate a resultant field that provides for the complex angle of incidence at least at a Hankel crossover distance from the guided surface waveguide probe P₃ as described above. Stated further, the charge terminal T₁ elevated over the terrestrial medium or the lossy conducting medium is configured to generate at least one resultant field that synthesizes a wave front incident at the complex Brewster angle of incidence (θ_(i,B)) of the terrestrial medium or the lossy conducting medium. The complex angle of incidence or complex Brewster angle of incidence may be calculated as described above.

According to the various embodiments, the guided surface wave that embodies the amplitude modulated signal decays exponentially as a function of distance from the guided surface waveguide probe P₃. In this respect, the guided surface wave that embodies the amplitude modulated signal is a transmission line mode. Consequently, receivers such as an AM radio will load the guided surface waveguide probe P₃ and the AM transmitter 403 coupled thereto through the matching network 406. However, given that the typical AM radio is locally powered, the electrical load that such a receiver will present to the guided surface waveguide probe P₃/AM Transmitter 403 is very small if not negligible as was discussed above. Given this reality, it would not be possible to come up with enough receivers to present much of a change in the electrical load presented by AM receivers for the AM transmitter 402 and the guided surface waveguide probe P₃. Thus, ultimately, the electrical load seen by the AM transmitter 403 and the guided surface waveguide probe P₃ is likely to be relatively constant and primarily involves resistive losses in the ground and in the components that make up the AM transmitter 403, the matching network 406, and the guided surface waveguide probe P₃ itself.

Given that the electrical load experienced by the guided surface waveguide probe 2006 a is not likely to fluctuate significantly, as the conductivity and permittivity of the ground changes over time as discussed above, the waveguide probe control system 479 can be configured to adjust the taps by controlling the switching mechanism 476 using the current at the ground stake 456 as detected by the ammeter 459 as feedback in order to optimize the launching of the guided surface wave. The taps may be adjusted in order to maximize current at the ground stake 456 to ensure optimal operation in view of changing ground conditions. In embodiments where field readings are provided by the field meter 469 as feedback to the waveguide probe control system 479, the taps may be adjusted to maintain a predefined field strength of the fields created by the guided surface wave.

As an alternative, the waveguide probe control system 479 may obtain a feedback signal from a ground parameter meter that provides real time values of conductivity and permittivity for the ground local to the guided surface waveguide probe P₃ as described above. The waveguide probe control system 479 may select a tap so that the physical configuration of the guided surface waveguide probe P₃ substantially matches an optimal configuration of the guided surface waveguide probe P₃ as calculated from the values of conductivity and permittivity of the ground at the site of the guided surface waveguide probe P₃.

According to one embodiment, amplifier 419 or other appropriate component of the AM transmitter 403 is controlled to drive the output AM signal 433 in a manner so as to maintain a constant voltage on the charge terminal T₁. Since the strength of the resulting electromagnetic field embodied in the guided surface wave launched by the guided surface waveguide probe P₃ is proportional to the voltage on the charge terminal T₁, the voltage level maintained will depend upon the ultimate desired strength of the electromagnetic field of the guided surface wave. Note that where the conductivity and permittivity of the ground changes, the efficiency of the guided surface waveguide probe P₃ in launching the guided surface wave may increase or decrease accordingly. As such, the waveguide probe control system 479 is configured to maintain optimum launching efficiency with respect to launching the guided surface wave so that energy is not lost by driving the output AM signal 433 with more power via the amplifier 419 than should be necessary to maintain the desired field strengths. In other words, if the launching efficiency of the guided surface waveguide probe P₃ is compromised and the amplifier 419 works harder to maintain the desired voltage and field strength, then it may be the case that energy is unnecessarily being wasted in the system. To this end, it is also possible that a feedback signal may be generated based on the magnitude of power, current, or other parameter indicating a degree of the output produced by the amplifier 419 or other component in driving the guided surface waveguide probe P₃, where the expected electrical load experienced by the guided surface waveguide probe P₃ and the AM transmitter 403 is to remain relatively constant. If the amount of power supplied to the guided surface waveguide probe P₃ and the AM transmitter 403 exceeds expected values, then the launching efficiency may not be optimum and adjustment of the taps via the switching mechanism 476 may be desirable. Alternatively, other parameters of the guided surface waveguide probe P₃ might be adjusted.

Referring next to FIG. 25, shown is still another example of a modulated transmission system comprising an Amplitude Modulation (AM) transmission system 400 d according to one embodiment of the present disclosure. The AM transmission system 400 d is yet another example of the AM transmission system 400 (FIG. 21) described above. The AM transmission system 400 d includes the AM transmitter 403, the matching network 406, and a guided surface waveguide probe P₄ that is similar to the guided surface waveguide probe 200 f (FIG. 17). The AM transmitter 403 is the same as was described with reference to FIG. 21 and includes the carrier source 413, the information signal source 416, the AM subsystem 409, the amplifier 419, and potentially other components as described above. Accordingly, a detailed discussion of the operation of the AM transmitter 403 is not provided with reference to FIG. 25 as the same is set forth in the discussion of FIG. 21 above.

The guided surface waveguide probe P₄ is a poly-phase probe that includes a first charge terminal T₁ and a second charge terminal T₂. The guided surface waveguide probe P₄ further includes a roller mechanism 483. The guided surface waveguide probe P₄ further includes a coil 486. The roller mechanism 483 contacts the coil 486 in a continuous manner and varies its position as can be appreciated so that the position where the charge terminal T₁ is electrically coupled to the coil 486 may vary accordingly.

The roller mechanism 483 is part of a roller inductor that is one example of a variable inductor that may be used. Alternatively, a switching mechanism 463 (FIG. 23) as described above may be employed. A free end of the coil 486 is coupled to the second charge terminal T₂. The input of the roller mechanism 483 is coupled to the first charge terminal T₁. As an alternative, the input of the roller mechanism 483 may be coupled to the second charge terminal T₂ and a free end of the coil 486 may be coupled to the first charge terminal T₁. In the end, the use of the roller mechanism 483 facilitates varying the length of the coil 486 coupled between the first charge terminal T₁ and the second charge terminal T₂. The coil 486 provides one example of a phase delay circuit that may be used in the feed network of the guided surface waveguide probe P₄. It is understood that other phase delay circuits may be employed as mentioned above.

The guided surface waveguide probe P₄ includes a waveguide probe control system 489. The waveguide probe control system 489 generates a control output that is applied to control the position of the roller mechanism 483 on the coil 486. In addition, the signal output of a field meter 469 may be coupled to a feedback input of the waveguide probe control system 489. Alternatively, the signal output of a ground parameter meter 493 may be coupled to a feedback input of the waveguide probe control system 489.

According to one embodiment, the AM transmitter 403 is inductively coupled to the guided surface waveguide probe P₄ through matching network 406. However, it is understood that the AM transmitter 403 and matching network 406 may be directly coupled to the guided surface waveguide probe P₄, where such inductive coupling to the guided surface waveguide probe P₄ is shown as an example.

The amplitude modulation transmission system 400 d operates in a manner similar to the amplitude modulation transmission system 400 (FIG. 21) described above. To this end, the amplifier 419 or other appropriate component of the AM transmitter 403 drives the output AM signal 433 that is applied to the guided surface waveguide probe P₄ through the matching network 406. In one embodiment, the waveguide probe control system 489 receives feedback from the field meter 469 and operates to generate a guided surface wave with desired field strengths. Alternatively, the waveguide probe control system 489 may obtain a signals from a ground parameter meter 493 that provides current values of conductivity and permittivity for the ground local to the guided surface waveguide probe P₄ as described above. The guided surface waveguide probe P₄ may be adjusted to substantially match an optimal configuration of the guided surface waveguide probe P₄ as calculated from the values of conductivity and permittivity of the ground at the site of the guided surface waveguide probe P₄ as set forth above. In addition, the waveguide probe control system 489 may receive a feedback signal generated from the power output of the amplifier 419 or other appropriate component of the AM transmitter 403 that indicates the power supplied to the guided surface waveguide probe P₄.

Based on one or more of these feedback parameters, the waveguide probe control system 489 controls the position of the roller mechanism 483 to maximize the launching efficiency of the guided surface wave and, correspondingly, minimize the magnitude of the power supplied by the amplifier 419 while maintaining a desired voltage on the first or upper charge terminal T₁ and/or the desired field strength associated with the resulting guided surface wave launched. The waveguide probe control system 489 may further take into account that the electrical load perceived by the guided surface waveguide probe P₄ is likely to be negligible and relatively constant as described above.

With reference to FIG. 26, shown is an illustration of skywave propagation from a conventional antenna. Specifically, as radiated electromagnetic fields propagate from a source antenna 503, they will refract off of the ionization layer 506 in the sky and propagate back to the ground some distance from the source antenna 503. In this respect, there is a skywave propagation path 509 and a ground wave propagation path 513 associated with a skywave. Generally, this effect is more pronounced at night given the effect of solar radiation on the ionization layer during the day. Also shown is the virtual height Hv of the ionization layer 506.

According to the various embodiments, the guided surface waveguide probes described herein are anti-skywave structures. That is to say, the guided surface waveguide probes P launch the guided surface waves embodying modulated signals as described herein while minimizing or eliminating the creation of any skywave. This is due to the nature of the guided surface waves in that they are bound to the surface of the earth or terrestrial medium. Thus, modulated signals such as AM signals may be transmitted using a guided surface waveguide probe without the concern of creating problematic skywaves. To the extent that any radiated fields are created by a given guided surface waveguide probe P, such radiated fields are likely to be relatively small or negligible provided that the guided surface waveguide probe P is electrically small as described above. As a consequence, one may transmit a modulated signal in the form of a guided surface wave as described herein without having to reduce the power of transmission at nighttime to prevent skywave interference with other stations.

In addition, with reference to the various embodiments described above in FIGS. 21-26, various shielding techniques may be employed to further reduce any radiation, however minimal, that might be generated by the various embodiments of the guided surface waveguide probes P described herein.

Referring next to FIG. 27, shown is a drawing that provides an illustration of first and second guided surface wave (GSW) field strength curves 2096 a and 2096 b associated with of a pair of guided surface waves generated by a corresponding pair of guided surface waveguide probes as described above. The GSW field strength curves 2096 a/b show field strengths as a function of distance as can be appreciated. Also depicted are radiated field strength curves 2097 a/b that show example field strengths of radiated fields generated by conventional antennas. To this end, the respective guided surface waveguide probes are positioned so that their areas of transmission overlap in a predefined manner. According to various embodiments, the field strengths and physical separation of the respective guided surface waveguide probes are specified so that a predefined overlap is achieved such that a first AM signal embodied in the first guided surface wave does not substantially interfere with a second AM signal embodied in the second guided surface wave.

As mentioned above, each of the GSW field strength curves 2096 a/b of the respective guided surface waves decay exponentially as a function of e^(−αd)/√{square root over (d)} (see above) where d is the distance from the respective guided surface waveguide probes. This is because such guided surface waves comprise transmission line modes as mentioned above. As such, the GSW field strength curves 2096 a/b each have the characteristic knee as described above.

It should be noted that the spreading factor for a radiated field is a function of 1/r, where r is distance. However, the spreading factor for a guided surface wave is a function of 1/√{square root over (r)}. A radiated field spreads hemispherically whereas a guided surface wave is bound to the waveguide which is the lossy conducting medium or the ground. As a consequence, a guided surface wave has a much smaller spreading factor that translates into a stronger signal before the knee of the curve defined by the exponential decay. In addition, the exponential decay of the guided surface wave means that there is a more defined signal cutoff beyond the characteristic knee of the field strength curve as described above. As a consequence, the signal strength of a guided surface wave is stronger before the knee and the relatively abrupt cutoff due to the exponential decay means that the possibility of interference with other transmitted signals is reduced.

Specifically, due to the fact that the GSW field strength curves 2096 a/b associated with guided surface waves launched by a guided surface waveguide probe decay exponentially, it is possible to place two different service areas relatively close without substantial interference. Such is the case even if the frequencies of transmission are the same for both guided surface waveguide probes.

To illustrate, assume that two different guided surface waveguide probes are configured to transmit guided surface waves embodying AM signals, where the guided surface waves have field strengths that are equal in magnitude at respective distances from the corresponding guided surface waveguide probes. Each GSW field strength curve 2096 a/b includes a service contour SC that is located at a distance from the originating guided surface waveguide probe having a field strength at a predefined threshold considered appropriate to avoid interference with various other radio signals, fields generated by local electrical equipment, and other sources of interference. In one embodiment, such a threshold may be set at 0.5 millivolts per meter (mV/m) other appropriate threshold. This threshold defines a service contour SC of a respective transmitting structure.

To the extent that adjacent GSW field strength curves 2096 a/b overlap, the second field strength of a second guided surface waveguide probe must be specified so as to have a field strength that is below a predefined threshold at the service contour SC associated with the first guided surface waveguide probe so as to avoid any substantial interference with the AM signal represented by the first guided surface waveguide probe.

According to one convention, such a predefined threshold is set at 1/20^(th) the field strength of the first guided surface waveguide probe. That is to say, in one embodiment, where the field strength of the first GSW field strength curve 2096 a is equal to 0.5 mV/m, the field strength of the second GSW field strength curve 2096 b associated with a second adjacent guided surface waveguide probe must be less than or equal to a value that is twenty times less than 0.5 mV/m which translates to 0.025 mV/m in order to avoid unacceptable interference between the respective signals. The point at which a given GSW field strength curve 2096 b has a strength at the 0.025 mV/m may be termed the interference contour IC of a given guided surface waveguide probe. One advantage, among others, to the use of guided surface waves for the transmission of AM signals is that the signal strength of such signals for much of a given service area is much stronger than can be created via conventional antennas. As such, it is possible to increase the signal-to-noise ratio of AM signals. Given the fact that guided surface waves have the characteristic knee, the distance between the service contour SC and the interference contour IC for a given guided surface waveguide probe is much less than the same distance for a radiated field generated by a conventional quarter wave antenna.

As shown in FIG. 27, the fact that the distance between the service contour SC and the interference contour IC for a given guided surface waveguide probe is much less than the same distance for a radiated field generated by a conventional quarter wave antenna means that more area may be covered by respective guided surface waveguide probes and the respective service areas can be closer together without unacceptable interference.

As shown in FIG. 27, a first guided surface waveguide probe 3003 a is positioned adjacent to a second guided surface waveguide probe 3003 b. The fact that the distance between the respective service contours SC_(Sa/b) and their counterpart interference contours IC_(Sa/b) (where “S” refers to “surface” for a guided surface wave) is much reduced, the area of interference between such adjacent probes is relatively small. This compares favorably with the distance between the service contours SC_(Ra/b) and interference contours IC_(Ra/b) of radiated fields represented by the radiated field strength curves 2097 a/b. Specifically, the service contours SCRa/b are much closer to the position of a corresponding radiating antenna (not shown) located at the same position as the guided surface waveguide probes 3003 a/b. Thus, the guided surface waveguide probes 3003 a/b provide a much larger area of service with much reduced areas of interference relative to conventional antennas.

Referring next to FIG. 28, shown are service areas 3006 associated with three different guided surface waveguide probes transmitting guided surface waves embodying AM signals. As shown, a network of adjacent service areas may be specified with distances between service contours SC and interference contours IC being relatively small with respect to the entire effective area of service. As such, it would be possible to create a honeycomb or other arrangement of service areas associated with guided surface waveguide probes transmitting guided surface waves embodying AM signals to provide superior coverage of a given area.

It should be emphasized that the above-described embodiments of the present disclosure are merely possible examples of implementations set forth for a clear understanding of the principles of the disclosure. Many variations and modifications may be made to the above-described embodiment(s) without departing substantially from the spirit and principles of the disclosure. All such modifications and variations are intended to be included herein within the scope of this disclosure and protected by the following claims. In addition, all optional and preferred features and modifications of the described embodiments and dependent claims are usable in all aspects of the disclosure taught herein. Furthermore, the individual features of the dependent claims, as well as all optional and preferred features and modifications of the described embodiments, are combinable and interchangeable with one another. 

Therefore, the following is claimed:
 1. A system, comprising: a guided surface waveguide probe; a modulation circuitry coupled to the guided surface waveguide probe, the modulation circuitry being configured to generate a modulated signal, the modulated signal being applied to the guided surface waveguide probe; and the guided surface waveguide probe being adjusted to launch a guided surface wave along a terrestrial medium, the guided surface wave embodying the modulated signal.
 2. The system of claim 1, wherein the modulation circuitry further comprises an amplitude modulation circuitry, and the modulated signal further comprises an amplitude modulation signal.
 3. The system of claim 1, wherein the guided surface waveguide probe is a polyphase waveguide probe having at least two charge terminals.
 4. The system of claim 1, wherein the guided surface waveguide probe comprises a charge terminal elevated over the terrestrial medium configured to generate at least one resultant field that synthesizes a wave front incident at a complex Brewster angle of incidence (θ_(i,B)) of the terrestrial medium at a vicinity of the guided surface waveguide probe.
 5. The system of claim 1, wherein the guided surface waveguide probe is a single phase probe having a single charge terminal.
 6. The system of claim 5, wherein the guided surface waveguide probe further comprises a feed network electrically coupled to the single charge terminal, the feed network providing a phase delay (Φ) that matches a wave tilt angle (W) associated with a complex Brewster angle of incidence (θ_(i,B)) associated with the terrestrial medium in a vicinity of the guided surface waveguide probe.
 7. The system of claim 5, wherein the guided surface waveguide probe further comprises a compensation terminal.
 8. The system of claim 1, wherein the guided surface wave decays exponentially as a function of a distance from the guided surface waveguide probe.
 9. The system of claim 1, wherein the guided surface waveguide probe further comprises an anti-skywave structure.
 10. The system of claim 1, wherein the modulation circuitry is directly coupled to a circuit component of the guided surface waveguide probe.
 11. The system of claim 1, wherein the modulation circuitry is inductively coupled to a circuit component of the guided surface waveguide probe.
 12. The system of claim 1, wherein the modulation circuitry further comprises amplitude modulation circuitry, and a modulation type performed by the amplitude modulation circuitry is taken from a group consisting of a double-sideband full carrier, a single-sideband reduced-carrier, a single-sideband full-carrier, single-sideband suppressed-carrier, an independent-sideband emission, a vestigial-sideband, or a linked compressor and expander.
 13. A method, comprising: coupling an amplitude modulated signal to a guided surface waveguide probe; and launching a guided surface wave embodying the amplitude modulated signal via the guided surface waveguide probe, wherein the guided surface wave decays exponentially as a function of a distance from the guided surface waveguide probe.
 14. The method of claim 13, wherein the guided surface wave is launched while minimizing creation of a skywave.
 15. The method of claim 13, wherein the guided surface wave propagates along an interface of an atmospheric medium and a terrestrial medium.
 16. The method of claim 13, wherein the guided surface waveguide probe further comprises a single phase waveguide probe having a charge terminal and a feed network electrically coupled to the charge terminal, and the step of launching the guided surface wave via the guided surface waveguide probe further comprises the step of generating a resultant field that matches a wave tilt angle (Ψ) associated with a complex Brewster angle of incidence (θ_(i,B)) associated with a terrestrial medium in a vicinity of the guided surface waveguide probe.
 17. The method of claim 13, wherein the guided surface waveguide probe comprises at least one charge terminal elevated over a terrestrial medium, and the step of launching the guided surface wave via the guided surface waveguide probe along the terrestrial medium further comprises the step of generating at least one resultant field that synthesizes a wave front incident at a complex Brewster angle of incidence (θ_(i,B)) of the terrestrial medium at a vicinity of the guided surface waveguide probe.
 18. The method of claim 13, further comprising generating the amplitude modulated signal.
 19. A system, comprising: means for generating a modulated signal; and means for launching a guided surface wave embodying the modulated signal along an interface of an atmospheric medium and a terrestrial medium, wherein the guided surface wave decays exponentially as a function of a distance from said means for generating modulated signal.
 20. The system of claim 19, wherein the means for launching the guided surface wave generates a resultant field that matches a wave tilt angle (Ψ) associated with a complex Brewster angle of incidence (θ_(i,B)) associated with the terrestrial medium in a vicinity of a site of the launching of the guided surface wave.
 21. The system of claim 19, wherein the means for launching the guided surface wave generates at least one resultant field that synthesizes a wave front incident at a complex Brewster angle of incidence (θ_(i,B)) of the terrestrial medium at a vicinity of a site of the launching of the guided surface wave.
 22. An apparatus, comprising: a guided surface waveguide probe having a charge terminal and a feed network coupled to the charge terminal, the feed network including a phase delay circuit positioned adjacent to the charge terminal; modulation circuitry coupled to the guided surface waveguide probe, the modulation circuitry being configured to generate a modulated signal, the modulated signal being applied to the guided surface waveguide probe; and the guided surface waveguide probe being adjusted to launch a guided surface wave along a terrestrial medium, the guided surface wave embodying the modulated signal.
 23. The apparatus of claim 22, wherein the feed network further comprises a conductor, a first end of the conductor being coupled to the phase delay circuit, and a second end of the conductor being coupled to an output of the modulation circuitry.
 24. The apparatus of claim 23, wherein the feed network further comprises a feed line coupling the phase delay circuit to the charge terminal.
 25. The apparatus of claim 23, wherein the phase delay circuit further comprises a coil, and the conductor is coupled to a tap on the coil.
 26. The apparatus of claim 23, wherein the phase delay circuit further comprises a coil, and the conductor is coupled to an end of the coil.
 27. The apparatus of claim 22, wherein: the feed network further comprises a conductor, a first end of the conductor being coupled to a ground stake, and a second end of the conductor being coupled to the modulation circuitry; and an output of the modulation circuitry is coupled to the phase delay circuit.
 28. The apparatus of claim 22, wherein the phase delay circuit further comprises a reactive component. 